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AD-A112 725 DAYTON UNIV ON RESEARCH INST F/S l1/4EXPERIMENTAL AND NUMERICAL ANALYSIS OF AXIALLY C014RESSED CIRCU-(ETC(U)OCT Al N R GAULO F33615-79-C-3030
UNCLASSIFIED AFWAL-TR-8-3158 NL
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AFWAL-TR-81-3158
EXPERIMENTAL AND NUMERICAL ANALYSIS OF AXIALLY COMPRESSEDt-3 CIRCULAR CYLINDRICAL FIBER-REINFORCED PANELS WITH VARIOUS
BOUNDARY CONDITIONS
i NELSON R. BAULD, JR.
S CLEMSON UNIVERSITYCLEMSON, SC 29631
OCTOBER 1981
TECHNICAL REPORT AFWAL-81-3158Final Report for Period 1 October 1978 - 30 September 1981
Approved for public release; distribution unlimited.
DTCD.
FLIGHT DYNAMICS LABORATORY "_.Uj AIR FORCE WRIGHT AERONAUTICAL LABORATORIES_.-. AIR FORCE SYSTEMS COMMAND_ WRIGHT-PATTERSON AIR FORCE BASE, OHIO 45433
S0 032
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NOTICE
When Government drawings, specifications, or other data are used for anypurpose other than in connection with a definitely related Governmentprocurement operation, the United States Government thereby incurs noresponsibility nor any obligation whatsoever; and the fact that thegovernment may have formulated, furnished, or in any way supplied the saiddrawings, specifications, or other data, is not to be regarded by implicationor otherwise as in any manner licensing the holder or any other person orcorporation, or conveying any rights or permission to manufacture use, orsell any patented invention that may in any way be related thereto.
This report has been reviewed by the Office of Public Affairs (ASD/PA) and isreleasable to the National Technical Information Service (NTIS). At NTIS, itwill be available to the general public, including foreign nations.
This technical report has been reviewed and is approved for publication.
NARENDRA S. KHOT FREDERICK A. PICCHIONI, Lt Col, USAFProject Engineer Chief, Analysis & Optimization Branch
FOR THE COMMANDER
RALPH L. KUSTER, JR., Col, USAFChief, Structures & Dynamics Div.
If your address has changed, if you wish to be removed from our mailinglist, or if the addressee is no longer employed by your organization pleasenotify AFWAL/FIBR , W-PAFB, OH 45433 to help us maintain acurrent mailing list
Copies of this report should not be returned unless return is required bysecurity considerations, contractual obligations, or notice on a specificdocument.
AIR FORCE/56780/18 March 1982 - 200
l . . . .. .. . .. . . . . . . . . . , . . . . . .. ,,, .. . . ... _ . . .. . . .. . . . . , .. i
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UNCLASSIFIEDSECURITY CLASSIFICATION OF THIS PAGE (When Dala.Entered)
REPORT DOCUMENTATION PAGE READ INSTRUCTIONSBEFORE COMPLETING FORM
I. REPORT NUMBER 2. kOVT ACCESSION NO. 3 RECIPIENT'S CATALOG NUMBER
AFWAL-TR-81-3158 4fl-1~-~ -7. ____________
4. TITLE (and Subtitle) S TYPE OF REPORT & PERIOD COVERED
EXPERIMENTAL AND NUMERICAL ANALYSIS OF AXIALLY Final Report for Period
COMPRESSED CIRCULAR CYLINDRICAL FIBER-REINFORCED I October 1978-30 Sept 1981
PANELS WITH VARIOUS BOUNDARY CONDITIONS 6. PERFORMING O1G. REPORT NUMBER
7. AUTHOR(.) 8. CONTRACT OR GRANT NUMBER(I
Nelson R. Bauld, Jr.F33615-79-C-3030
9. PERFORMING ORGANIZATION NAME AND ADDRESS 10. PROGRAM ELEMENT. PROJECT. TASK
Clemson University AREA & WORK UNIT NUMBERS
Clemson, SC 29631 Proj 2307, Task 2307N5Work Unit 2307N501
It. CONTROLLING OFFICE NAME AND ADDRESS 12. REPORT DATE
University of Dayton October 1981Research Institute 13. NUMBER OF PAGES
Dayton, OH 45469 15114. MONITORING AGENCY NAME & ADDRESS(f different from Cont oiling Office) I5 SECURITY CLASS. (of this report)
Flight Dynamics Laboratory (AFWAL/FIBRA) UNCLASSIFIEDAir Force Wright Aeronautical Laboratories (AFSC) 1.. DECLASSIFICATION 0OWNGRAONG-Wright-Patterson AFB, Ohio 45433 SCHEDULE
16. DISTRIBUTION STATEMENT (of this Report)
Approved for public release, distribution unlimited.
17. DISTRIBUTION STATEMENT (of the abstract entered In Block 20, If different from Report)
I. SUPPLEMENTARY NOTES
It. KEY WORDS (Conllnue on reverse side If necessary ,nd identify by block number)
Buckling LoadComposite StructuresPlates and ShellsJ
Finite Difference Methods
Experiments
20. A STRACT (Continue On reverse side if neceesry and Identify by block nmber)
;OThis report presents comparisons between the experimental and numerical buck-ling behaviors of fiber-reinforced, circular cylindrical panels under pre-
scribed uniform end-displacements. Numerical predictions used in the compari-sons were obtained from the energy-based, finite-difference computer proqramCLAPP. Test specimens were clamped along both curved edges and were eithersimply supported or unsupported along the straight edges.,-
DD , 4JAN 73 EDITION OF INOV SS IS OBSOLETE UNCLASSIFIED
SECURITY CLASSIFICATION OF THIS PAGE ('When Dai Fnt-red)
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FOREWORD
This report was prepared by Dr Nelson R. Bauld, Jr., Professor,Department of Mechanical Engineering, Clemson University, Clemson,South Carolina, in partial fulfillment of the requirements underContract F33615-79-C-3030. The effort was initiated under ProjectNo. 2307, "Research in Flight Vehicle Structures," Task 2307N501,"Basic Research in Structures and Dynamics." The project monitorfor the effort was Dr Narendra S. Khot of the Structures and DynamicsDivision (AFWAL/FIBRA).
The technical work was performed during the period October 1978through September 1981. Review report was submitted in October 1981and the final report in January 1982.
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TABLE OF CONTENTS
Section Page
I INTRODUCTION
II TESTING PROCEDURE 3
1. Test Specimens 3* Program A 4
Program B 52. Test Fixture 53. Testing Machine 94. Imperfection Device 105. Positioning of Head-Plate and Base-Plate 12
6. Specimen Installation 14
IIl EXPERIMENTAL DATA 17
1. Initial Geometric Imperfections 172. Strain Measurements 18
Program A 18* Program B 18
3. End-Shortening 21
4. Buckling Behaviors 21
IV EXPERIMENTAL AND NUMERICAL RESULTS 22
I. Analysis of Results of Testing Program A 22* Specimens with simply-supported 22
straight edgesSpecimens with unsupported straight 25edges
2. Analysis of Results of Testing Program B 35Specimens with simply-supported 35edgesSpecimens with unsupported straight 40
edges
V LONGITUDINAL STIFFENERS 45
I. Introduction 452. Stiffener Strain Energy 46
3. Stiffener Energy in Matrix Form 474. Displacement Continuity 495. Finite-Difference Considerations 526. Incorporation into CLAPP 597. Quasi-Isotropic Fiber-Reinforced Stiffeners 6O
-I-AECEDi PAGJE BLAW-NOT fl1.4ML V
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Appendix Page
A Strain, End-shortening, and Imperfection 68Measurements for Test Panels withSimply-Supported Straight Edges andClamped Curved Edges. Testing Program A.
B Strain, End-shortening, and ImperfectionMeasurements for Test Panels with 93Unsupported Straight Edges and ClampedCurved Edges. Testing Program B.
C Strain, End-shortening, and ImperfectionMeasurements for Test Panels for Testing 118Proqram B
D User's Manual for Computer Program CLAPP 133
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LIST OF ILLUSTRATIONS
Figure Page
I Geometry of curved panel specimen. 3
2 Head-plate and base-plate with auxilliary pressureblocks and clamping devices. 5
3 Testing fixture installed in the Tinius-Olsenhydraulic testing machine. 9
4 Imperfection measuring device attached to thebase-plate of the testing fixture. 10
5 Imperfection measuring device in position tomeasure initial geometrical imperfections of aspecimen. 11
6 Device used to establish the relative parallelismof the head-plate and the base-plate of thetesting fixture. 12
7 Test specimen installed in base-plate and bookendsthat supply simply-supported edge conditions. 15
8 Simply-supported edge of a test specimen showingvertical pressure blocks. 16
9 Simply-supported specimen partially installed in
the testing fixture and associated strainmeasuring equipment. 19
10 Numerical and experimental load versus end-shortening curves for a 16 in. x 16 in. panelwith simply-supported straight edges. 26
1l Analytical and numerical load versus end-shortening curves for panels with simply-supportedstraight edges. 27
12 Experimental strains corresponding to prescribedvalues of end-displacement for a panel with simply-supported straight edges and constrained circumfer-ential displacements. 28
13 Analytical nodal loads corresponding to prescribedvalues of end-shortening for a specimen with simply-supported straight edges with constrained circumfer-ential displacements. 29
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14 Analytical and experimental load versus end-
shortening curves for the perfect and imperfect
panel with unsupported straight edges. 32
15 Experimental strains corresponding to prescribedvalues of end-shortening for test specimens with
unsupported straight edges. 33
16 Analytical nodal loads corresponding to prescribedbalues of end-shortening for an initial imperfec-
tion of the form W = 0.005 (1+cos 7e/a) for
specimen with unsupported straight edges. 34
17 Theoretical and experimental equilibrium paths
for simply supported test specimens for testingProgram B. 37
18 Analytical load versus deflection curves for theperfect and imperfect panel with simply-supportedstraight edges and unconstrained circumferential
displacements. 38
19 Theoretical and experimental equilibrium paths for
specimens of Program B with unsupported straightedges. 43
20 Equilibrium paths for the axially compressed panelwith unsupported straight edges. 44
21 General thin-wall open cross section. 48
22 Detail of coefficient matrix [PAS2]. 53
23 Typical stiffener elements and the local numberingsystem for the surrounding grid points. 54
24 Interoid stiffener element and its local numberscheme. 56
25 Geometric details of a fiber reinforced laminate. 63
26 Stiffener stress distribution. 63
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LIST OF TABLES
Table Page
I Experimental and numerical buckling results
for circular cylindrical panels, testing
program A.
2 Experimental and numerical buckling results
for circular cylindrical panels, testing
program B.
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SECTION I
INTRODUCTION
The principal purpose of this investigation is to provide a basis for
assessing the capability of the computer program CLAPP [l] to predict
buckling loads for fiber-reinforced, circular cylindrical panels under
prescribed uniform axial end-displacements.
Two testing programs were undertaken to accomplish this objective.
They are designated as Program A and Program B in this report.
Program A. Experimental buckling loads were determined for 20 specimens
having identical fiber patterns of [0/9012s and 20 specimens having iden-
tical fiber patterns of [0/+45/90] s . The specimens of a particular fiber
pattern were characterized geometrically by five different aspect ratios
and by two different sets of boundary conditions. The aspect ratios were
a/b = 1/2, 3/4, 1, 4/3, and 2, where a and b are the dimensions of the
projection of a panel into its base plane as shown in Figure 1. Boundary
conditions along the straight edges of a specimen corresponded to either
an unsupported edge or a simply-supported edge. For the simply-supported
edge a distinction between unconstrained and constrained circumferential
displacements is also made. Boundary conditions along the curved edges
corresponded to a clamped edge for all specimens.
Program B. Experimental buckling loads were determined for 6 specimens
with the same fiber pattern ([0/901 2s), the same aspect ratio (a/b = 1.247,
a = 16 in. and b = 12.83 in.), and the same boundary conditions (unsupported
straight edges and clamped curved edges). Similarly, experimental buckling
loads were obtained for 5 specimens with the fiber pattern [0/+45/90] s ,
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aspect ratio a/b = 4/3 (a = 16 in. and b = 12 in.), and boundary conditions
consisting of simply-supported straight edges and clamped curved edges.
A second purpose of this investigation is to modify the computer pro-
gram CLAPP so as to minimize the effort required to input necessary data.
This phase of this investigation is contained as a USER'S MANUAL in
Appendix D.
Finally, a third purpose is to modify CLAPP so that it can be used to
predict the buckling behavior of fiber-reinforced, circular cylindrical
panels and flat plates that are augmented by longitudinal stiffeners. This
is accomplished for isotropic stiffeners with a variety of cross sections
and for a quasi-isotropic stiffener with a hat shaped cross section.
2
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SECTION II
TESTING PROCEDURE
(Il-i). TEST SPECIMENS. Each of the circular cylindrical specimens of
Program A and Program B was laminated from graphite-epoxy, and each speci-
men was cured in a mold for which the external radius was )2 inches.(I)
The external radius of a specimen tended to be slightly less than 12 inches
upon removal from the mold. The thickness of a test specimen was taken as
an average of the thicknesses at 32 locations along a perimeter located
uniformly 1-1/2 inches from the exterior perimeter of the specimen. The
average thickness for each specimen of Program A is shown in column 2 of
Table 1. The average thickness for each specimen of Program B is shown
in column 2 of Table 2. Figure 1
indicates pertinent geometrical
parameters of a typical specimen.
TThe radius, R = 12.0 in., is the
aradius of a perfectly circular
panel installed in the testing
fixture, and the thickness shown ___
is the average thickness of a 0.038 in.
typical panel.
Laminate stiffness properties R=2. in.
were calculated by lamination .Figure 1. GEOMETRY OF CURVED
theory [2] using the following PANEL SPECIMEN
lamina properties:
(1) All specimens were fabricated and cut by the Air Force Flight DynamicsLaboratory, Air Force Wright Aeronautical Laboratories, Air Force SystemsCommand, Wright-Patterson Air Force Base, Ohio.
3
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E = 20,524 ksi, E = 1,333 ksi, G2 = 752 ksi, =12 0.335, and ) 2 =
0.022. E and E22 are Young's moduli of elasticity parallel and perpen-
dicular to the fiber direction, G12 is tht shearing modulus associated
with these two directions, and ,12 and -21 are Poisson ratios.
Program A. The specimens of Program A were distinguished by aspect ratio
(a/b), laminate fiber pattern, and boundary conditions.
Specimens having five different aspect ratios (a/b = 1/2, 3/4, 1, 4/3,
and 2) were tested. It is convenient to perceive of specimens that are
associated with a specific aspect ratio to form a group. Thus, five
separate groups of specimens are identifiable.
Each group of specimens consisted of two sub-groups: one sub-group
being associated with simply-supported straight edges, and one sub-group
being associated with unsupported straight edges. Boundary conditions
along the curved edges were clamped for all specimens in each group.
Two laminate fiber-patterns ([0/9012 and s
for each sub-group. Moreover, each member of each group was duplicated to
provide a means to assess repeatibility of experimental results.
From the foregoing discussion it will be observed that each group con-
tained eight specimens: four with simply-supported straight edges and
four with unsupported straight edges. Of the four specimens in a sub-
group (either simply-supported or unsupported straight edges) two were
characterized by a fiber-pattern of [0/90 1 2s and two were characterized
by a fiber-pattern of [0/+45/90] . The complete experimental effort
amounted to forty specimens. Table I has been organized to ref'ect the
foregoing classification of specimens.
4
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I
The physical dimensions of the base-planes (projected area of a specimen)
of the specimens associated with the five aspect ratios were 8 x 16, 12 x 16,
16 x 16, 16 x 12, and 16 x 3 (all dimensions are in inches). These dimen-
sions correspond to the inside dimensions of the specimens after installation
in the testing fixture.
Program B. As was stated in the introduction, the specimens of Program B
can be categorized into two groups: one group with fiber pattern [0/9012s'
aspect ratio 16/12.83 = 1.247, and unsupported straight edges; and one
group with fiber pattern [0/+45/90] s aspect ratio 16/12 = 4/3, and simply-
suported straight edges. The results of buckling tests on these specimen
are tabulated in Table 2.
(11-2). TEST FIXTURE. The testing fixture used in both testing programs
was a modification of a test fixture used by Wilkins [3]. Modifications
of the Wilkins' testing fixture were necessary to accommodate specimens of
different aspect ratios. Figure 2 _. I .
shows the head-plate and the base-
plate (with their auxilliary
pressure blocks and clamping
plates) through which an axial
compressive load was applied to
a specimen. All surfaces of the
head-plate, and of the base-
plate, were carefully machined
so that they were within 0.001 in.
of being parallel.FIGURE 2. Head-plate and base-plate with
auxiliary pressure blocks andclamping plates.
5
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(1-3). TESTING MACHINE. An axial compr(,ssive load was appli ed to a ,pcci-
men through a 120,000 lb Tinius-Olsen hydraulic te.-,ting machine. Most experi-
mental buckling loads were of such a magni tudt that the intermediate ranqe
(12,000 lb range) of the testinq machine could be ned effectively. The
finest division for this range is 50 lb. The low range (3000 lb ranqe) wau
used to test several specimens with unsupported straight edges. The finest
division for this raniye is 5 lb.
The surfaces of the platten and the cross-head of the testing machine
were dressed so that they were nearly plane.
The head-plate and the base-plate of the testing fixture are shown
installed in the Tinius-Olsen testing machine in Figure 3.
Early in testing
Program A it became
apparent that the
cross-head would
tilt as the reactive
force of the speci-
men on the cross-head
tended to lift it off
the threads of the
vertical columns. To
eliminate the tilting
action two large
aluminum nuts were
machined and placed FIGURE 3. Test i ng Ii xt ure inta, it i n the Tin i,,-h 1 sen hyd raul I i c ttI i rM mal i ne.
on the vertical screws
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beneath the cross-head. At an appropriate point during the installation
of a specimen these nuts were tightened against the lower surfaces of the
cross-head causing it to lock in place. These aluminum locking nuts are
shown in Figure 3.
(11-4). IMPERFECTION DEVICE. Figure 4 shows the mechanical device that
was used to measure deviations of a specimen from a perfect cylindrical
form; that is, to measure the initial geometric imperfections of a speci-
men.
Components of this device were constructed so that the vertical sides
of the circular groove in the platform of the device were concentric with
the vertical sides of the circular groove in the base-plate of the testing
fixture. The imperfection device
was secured to the base-plate of
the testing fixture so that its
slotted vertical platform-
supports were perpendicular
to the base-plate. This en-
sured concentricity of the
platform groove with the groove
in the base-plate for any
platform level.
To position the imperfec-
tion device relative to the
base-plate of the testing
fixture, the dial indicator
mechanism shown in Figure h FIGURE 4. Imperfection measurinq device
attached to the'base-plate ofthe testing fixture.
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was designed so that it could be moved smoothly and snugly in the circular
groove of the platform of the imperfection measuring device. With the tip
of the dial indicator extension resting against the vertical side of the
circular groove in the base-plate, the mechanism was moved along the plat-
form groove. By trial the imperfection measuring device was adjusted rela-
tive to the base-plate so that the pointer of the dial indicator was undis-
turbed for a complete cycle along the platform qroove. Once the proper
position was located the imperfection measuring device was secured to the
base-plate of the testing fixture by machine bolts. Positioning pins were
installed so that the correct position could be duplicated. This procedure
resulted in a variation of less than 0.001 in. for a conplce trav'erse oi
the platform groove.
Holes for positioning pins were drilled at one-inch intervals along ,he
slotted vertical platform supports. This ensured that the position of the
imperfection measuring
device relative to the
base-plate of the testing
fixture could be duplicated
at appropriate levels.
Once the platform was lo-
cated at a specified level
by the posit ioninq pins,
it was locked in that
position by cap screws.
Figure 5 shows the
imperfection measuring FIGURE 5. Imperfection measurinq device inposition to measure initial qeometric
imperfections of a specimen.
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device installed on the testing fixture. Deviation of a specimen from per-
fect circularity were measured by movinu the dial indicator mechanism along
the platform qroove.
(11-5). POSITIONING OF HEAD-PLATE AND BASE-PLATE. Two requirements were
essential for proper alignment of the head-plate relative to the base-
plate of the testing fixture. First, the circular arc associated with an
edge of the circular groove in the head-plate and the correspondino cir-
cular arc of the circular groove in the base-plate must lie in parallel
planes. This requirement is realize -.": the head-plate (when attached
to the cross-head ot the testir., r , and the base-plate (when attached
to the platten of the testinq r c ire parallel. Secondly, these two
arcs must lie in a conmmon clrc 1 ndrical surface that is perpendi-
cular to the base-plate (and, hencie, p.,erpendicular to the head-plate).
Parallelism of the heaJ-
plate and the base-plate was
assessed using the device
shown in Figure 6. This
device cons;ists of a rigid
base that was machined to
fit snugly in the circular
groove of the base-plate,
and that could be moved
smoothly along the groove.
A dial indicator was
attach'd to a 'tiff -t, FIGURE 6. DeviCe ued to etabli,,h the relative
rod which was, Cilr. 1 ( lt i sm of tit, head-plate atnd thewo n c w a, a fixeu tst-plate o-f tit, tet i in t iX IJre
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the moveable base. With the plunger of the dial indicator resting against
the surface of the circular groove in the head-plate, the device was moved
along the circular groove in the base-plate. Using the centerline of the
circular groove as a reference, it was observed that the variation in the
distance between the surfaces of the grooves in the head-plate and the
base-plate did not exceed 0.0035 in. on either side of the centerline for
the maximum arc of 18.5 in. (circumferential arc length of the widest speci-
men). This variation was accordingly smaller for narrower specimens. Once
the head-plate and the base-plate had been assessed to be as parallel as
reasonable efforts would allow, they were securely clamped to the cross-
head and to the platten of the Tinius-Olsen testing machine by specially
designed clamps. These clamps can be seen in Figure 5.
The imperfection device was used to bring corresponding circular arcs
in the head-plate and in the base-plate into concentricity. To accomplish
this alignment the platform of the imperfection measuring device was posi-
tioned at an appropriate level and the tip of the dial indicator extension
shown in Figure 4e was allowed to rest against the vertical side of the
circular groove in the head-plate. Since the groove in the platform of the
imperfection measuring device is concentric with the vertical edge of the
circular groove in the base-plate, the corresponding edge of the circular
groove in the head-plate will be concentric with its counterpart in the
base-plate when the pointer of the dial indicator is undisturbed as the
indicator mechanism is moved smoothly along the platform groove. Thus,
appropriate alignment of the head-plate and the base-plate of the testing
fixture was accomplished.
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(11-6). SPECIMEN INSTALLATION. The procedure used to install specimens in
the testing fixture was similar for specimens with unsupported straight
edges and for specimens with simply-supported straight edges. It is con-
venient to describe the installation procedure for the specimens with
unsupported straight edges first, and, subsequently, describe the additional
installation features associated with the specimens for which the straight
edges were simply-supported. In either case the curved edges of all speci-
mens were clamped.
In preparation for buckling tests of specimens with unsupported straight
edges, a specimen was centered in the circular groove of the base-plate of
the testing fixture and the pressure blocks were adjusted by finger tightening
appropriate screws. The platten of the testing machine was then raised to
allow the upper curved edge of the specimen to enter the circular groove of
the head-plate to approximately three-quarters of the groove depth. Pressure
blocks in the head-plate were then adjusted by finger tightening appropriate
screws in the head-plate. Generators at several locations along the circum-
ference of a specimen were aligned vertically with a precision square. The
platten of the testing machine was then raised until the specimen experienced
a compressive force of 25 lb. Pressure blocks in the base-plate and in the
head-plate were adjusted to their final positions by applying a 40 in-lb
torque to appropriate screws while the 25 lb pre-load was maintained.
Preparation for buckling tests of specimens with a simply-supported
straight edges was similar to that for specimens with unsupported straight
edges. A specimen was centered in the circular groove of the base-plate
and its straight edges were inserted in the slots of the vertical edge
supports (hence forth referred to as book-ends) as shown in Figure 7.
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Pressure blocks in the base-plate and at each book-end were adjusted to
the finger tight position. The platten of the testing machine was then
raised to allow the upper curved edge of the specimen to enter the circular
groove of the head-plate to approximately three-quarters of the groove
depth. Pressure blocks in the head-plate were then adjusted to the finger
tight position. Generators
at several locations along
the circumference of the
specimen were aligned
vertically with a preci-
sion square. The platten
of the testing machine
was then raised until the
specimen experienced a
compressive force of 50 lb.
Pressure blocks in the
base-plate and in the head- FIGURE 7. Test specimen installed in the base-
plate and book-ends that supplyplate were adjusted to the simply-supported edge conditions.
40 in-lb position, and the
vertical pressure blocks in the book-ends (see Figure 8) were adjusted to
the finger tight position for specimens of Program A.
For Program B the pressure exerted on the specimen by the vertical
pressure blocks was adjusted to different amounts.
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FIGURE 8. Simply-supported edge of a test specimen
showing vertical pressure blocks.
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SECTION III
EXPERIMENTAL DATA
(Ill-l). INITIAL GEOMETRICAL IMPERFECTIONS. Initial deviations of a
specimen from a perfect cylindrical surface are referred to in this
report as initial geometric imperfections. Imperfection measurements
were obtained at the nodes of a rectangular grid drawn on the inner sur-
face of a specimen. Details of the imperfection grids for specimens
with different aspect ratios are listed in Appendices A and B for speci-
mens with simply-supported straight edges and unsupported straight edges,
respectively. This data corresponds to testing Program A. Details of
the imperfection grids used in testing Program B are listed in Appendix C.
For testing Program A, the reference point for imperfection measure-
ments lies on the specimen centerline two inches below the upper clamped
edge. Measurements were made at equal intervals on either side of the
specimen centerline, and at equal intervals along the generators of a
specimen. Measurements for specimens with unsupported edges were obtained
along these edges, while measurements for specimens with simply-supported
edges were obtained as close to the straight edges as the imperfection
measurinn device would permit. These observations are ref~ected in the
imperfection data contained in Appendices A and E. Actual spacing dimen-
sions for the imperfection grid associated wit'i each panel aspect ratio
are shown in these appendices also.
For testing Program B a specially constructed device, with two circu-
lar members that were concentric with the groove in base-plate, was used
to establish the reference point for imperfection measurements. Measure-
ments for imperfections were made at the locations described for Program A.
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Actual spacing dimensions for imperfection grids associated with panels
with unsupported straight edges and simply-supported straight edges are
indicated in Appendix C. The imperfection measurements for Program B are
also presented in Appendix C.
(111-2). STRAIN MEASUREMENTS. It was of interest to determine if the
axial compressive end-load was applied uniformly along the curved edges
of a specimen.
Program A. For testing Program A, axial strains were measured along an
arc lying one inch below the upper clamped edge on the specimen centerline
and at two other equally spaced points on both sides of the centerline.
Electrical resistance strain gages were bonded at identical locations on
both sides of a specimen so that, by means of an appropriate four-arm
bridge, only axial strains were sensed. Locations of the strain gages on
the surface nearest the center of curvature of a specimen can be observed
in Figure 7. Appendices A and B contain details for strain gage locations
for Program A.
Program B. For testing Program B, axial strains were measured atry' five
locations described in Program A for specimens with unsupported edges.
Axial strains were measured at only three locations for soecimens with
simply-supported edges: on the centerline and at two points symmetrically
located relative to the centerline. Appendix C contains details for strain
gage locations for Program B.
Strain gage readings were obtained using a Vishay/Ellis-20 digital
strain indicator and a Vishay-Ellis-21 ten channel switching and balancing
unit. This equipment is shown in Figure 9. Strain data associated with
18
''l h i ' -" ' i I I il i ... ... j
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r -•
testing Program A are 3 a a
presented in Appendix A
for specimens with simply-
supported straight edges,
and in Appendix B for
specimens with unsupported
straight edges. Strain
data associated with
testing Program B are
presented in Appendix C.
The strain data indi-
cates that the distribution FIGURE 9. Simply-supported specimen partiallyinstalled in the testinq fixture and
of force on the curved edge associated strain measuring equipment.
of a specimen is essentially
uniform in the very early
stages of the loading pro-
cess, but quickly becomes nonuniform. These observations remain valid for
all specimens in each testing program.
Consider specimens with unsupported straight edges. As was stated pre-
viously, specimens were not perfectly circular cylindrical as they emerged
from the mold. Consequently, installation in the testing fixture caused
regions near the ends to assume a circular cylindrical shape of radius 12
inches, while cross sections away from the ends assumed noncircular shapes
with the unsupported edges "dishing" toward the center of curvature. Gen-
erally, the centerline and generators in the regions on either side of the
centerline were straighter than generators near the edges. Since the axial
stiffness of a small strip of specimen parallel to a generator depends on
19
.. . . Ii ll . . . . . . . m.. .. ... . "" " n .. . l l I I I/ i n I I . . . .. . II, -j
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its flexural stiffness as well as its in-plane stiffness, the strains asso-
ciated with strips located at various sites on a specimen should be expected
to be different. Indeed, the non-uniformity of the strain distribution
should be expected to be intensified as the loading process proceeds. It is
noted, from the strain data for specimens with unsupported straight edges in
Appendix B, that the strains near the straight edges actually changed from
compression to tension during the early stages of loading. This reversal of
strain near the straight edges is associated with the bifurcation load for
the specimen under an essentially uniform end-load (as opposed to uniform
end-displacement). A more detailed discussion of this behavior is presented
in a later section.
Now consider specimens with simply-supported straight edges. These
specimens experienced the same "dishing" effects as specimens with unsupported
straight edges; however, the book-ends forced the edges to become straight
with the consequent configuration change on the interior of a specimen.
Accordingly, since these initial installed configurations occur in an essen-
tially random manner, nonuniform strain distributions should be expected
during the loading process.
Another possible reason for the nonuniform strain distributions exhibited
by specimens with simply-supported edges is the asymmetry in the axial dis-
placements that can be introduced at the book-ends. The strain distribution
on the interior of a specimen will deviate from uniformity if the axial dis-
placement distributions along the two simply-supported edges differ.
The further observation should be made that not only do the initial imper-
fections influence the buckling resistance of a specimen, but a certain unknown
initial stress distribution is associated with the installed initial configura-
tion that also influences the buckling resistance. The influence of the
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initial stress distribution on the buckling resistance is rather capricious.
The initial geometric imperfections that are incorporated in CLAPP assume
that the imperfect configuration is stress free.
(111-3). END-SHORTENING. The end-shortening of each specimen in testing
Programs A and B was measured with a dial indicator that was positioned so
as to determine the relative displacement between the platten and the
cross-head of the Tinius-Olsen testing machine. The axial compressive load
applied to the specimen was read directly from the testing machine. Load
and corresponding end-shortening data are listed in Appendices A and B for
specimens of testing Program A and in Appendix C for specimens of testing
Program B.
(111-4). BUCKLING BEHAVIORS. Experimental buckling loads for the 40 speci-
mens associated with testing Program A are listed in column 7 of Table 1
and those associated with the 10 specimens of testing Program B are listed
in column 5 of Table 2. The recorded experimental buckling load for each
specimen of either testing program was characterized by a distinct loss in
load carrying capacity. Loss of load carrying capacity was detected readily
from the load-dial of the Tinius-Olsen hydraulic testing machine, and was
always accompanied by a sudden shift in the equilibrium configuration of
the specimen that was clearly audible and visible.
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SECTION IV
EXPERIMENTAL AND NUMERICAL RESULTS
(IV-l). ANALYSIS OF RESULTS OF TESTING PROGRAM A. The theoretical buckling
loads shown in column 8 of Table 1 were calculated assuming that each panel
was subjected to a force that was uniformly applied along its curved edge.
The bifurcation branch of CLAPP was used to calculate these buckling loads.
Consequently, the theoretical buckling loads listed in Table 1 correspond
to bifurcation under a uniformly applied axial compression using both a 12
x 12 and a 20 x 12 finite difference grid. For this bifurcation analysis the
20 x 12 grid yielded a bifurcation load less than three percent smaller than
the 12 x 12 grid. Nevertheless, numerical calculations for the bifurcation
load for each of the remaining specimens were obtained using either a 20 x
12 or a 16 x 12 finite difference grid. The clamped boundary condition along
a curved edge of a specimen requires the transverse displacements be zero
along a line of nodal points coincident with the curved boundary and along
a parallel line of nodal points just inside the boundary. The larger num-
ber of grid points was always taken along the generators of a specimen to
minimize this internal constraint.
SPECIMENS WITH SIMPLY-SUPPORTED STRAIGHT EDGES. Table I shows that the bifur-
cation load predicted by CLAPP was greater than its corresponding set of
experimental buckling loads except for one specimen. The ratio of the modi
fied experimental load to the numerical bifurcation load is shown in the last
column of Table 1 for each specimen. The modified experimental buckling load
was obtained by assuming that the observed experimental buckling load was
uniformly distributed along the curved edge of a specimen and only the portion
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of the curved edge between the book-ends contributed to the buckling of a
specimen.
The ratio of the modified experimental buckling load to the theoretical
bifurcation load fell in the range 0.5 < p < 1.0 for eighteen of the twenty
specimens with simply-supported straight edges. The ratio was 0.458 for
one specimen and 1.072 for another. We remark that theoretical bifurcation
loads predicted by the energy method represent upper bounds to the classical
bifurcation loads associated with the test specimens. Moreover, in the
presence of initial geometric imperfections the experimental buckling loads
can be expected to be less than the classical bifurcation load if the speci-
ment is imperfection sensitive. If a specimen is not sensitive to initial
imperfections its experimental buckling load can be expected to compare
favorably with the theoretical bifurcation load.
Another complicating factor is the nature of the simply-supported boun-
dary condition. Actually two different types of the simply-supported boun-
dary conditions must be recognized. Normally, a simply-supported boundary
condition implies the bending moment and transverse displacement are zero.
In addition to these conditions, in-plane displacements or membrane forces
must be specified. Consequently, with reference to the simply-supported
test specimens, circumferential displacement can be prevented, can be
allowed to occur freely, or, there can be some intermediate partial restric-
tion of circumferential displacements. The theoretical bifurcation loads
listed in Table I correspond to freely occurring circumferential displace-
ments along the straight edges.
The foregoing observations are offered in explanation of the rather
large difference between the experimental buckling load and the theoretical
bifurcation load for some test specimens and the much better agreement
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between the two loads for other specimens. The ratio 1.072 for one test
specimen is believed to be a quirk arising out of the way the modified
experimental buckling load is defined.
Figure 10 shows the experimental and numerical load versus end-
shortening curves for a 16 in. x 16 in. panel with simply-supported
straight edges. The numerical load vs end-shortening curve was obtained
using measured initial imperfections. A plot of the normalized buckling
determinant is also shown in the figure. We note that the numerical curve
is essentially linear even though initial imperfections are present.
Furthermore, the panel buckled apparently by bifurcation as indicated by
the system buckling determinant becoming negative.
CLAPP was modified to provide the capability of prescribing uniform
end displacements as opposed to prescribing uniform end load.
Figure 11 shows the experimental and theoretical load versus end-
shortening curves for the 16 in. x 8 in. specimen with the [0/9032s fiber
pattern. The theoretical bifurcation loads for conceptual models with
simply-supported edges are 2522 lb when circumferential displacements occur
freely, and 4311 lb when circumferential displacements are prevented at the
straight edges. The experimental buckling loads for the two test specimens
are 2500 lb and 3240 lb.
Thcre is, perhaps, better agreement between the theoretical bifurcation
loads and the experimental buckling loads than is immediately obvious. Con-
sider the experimental curve labeled 1 in Figure 11. The urosual shape of
this load versus end-shortening curve appears to be the result of the panel
slipping circumferentially in the book-ends at a load near 300 lb. In this
test it becomes clear that the friction forces exerted by the vertical
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pressure blocks on the specimen was not sufficient to prevent circumferen-
tial displacements. Consequently, at approximately 300 lb the book-ends
allowed circumferential displacements to commence. However, the specimen
edges apparently made contact with back surfaces of the book-ends and
circumferential displacements were prevented from approximately 1500 lb
onward. One expects the experimental buckling load for this specimen to
fall between the two theoretical bifurcation loads.
The behavior exhibited by the experimental curve labeled 2 in Figure
11 can be explained in a similar manner. Initially the friction forces
exerted by the vertical pressure blocks on the specimen is sufficient to
prevent circumferential displacements. At a load of approximately 800 lb
a gradual slippage occurs and, finally at a load of approximately 2250 lb
the friction forces were not sufficient to prevent or restrict these dis-
placements any longer. A sudden slippage occurred that resulted in the
buckling of the specimen before its straight edges made contact with the
back surfaces of the book-ends. Accordingly, one expects the experimental
buckling load for this specimen to agree closely with the theoretical
bifurcation load corresponding to the simple-support condition when circum-
ferential displacements occur freely.
The experimental strain distribution shown in Figure 12 shows an en-
couraging resemblance to the calculated nodal load distribution shown in
Figure 13.
SPECIMENS WITH UNSUPPORTED STRAIGHT EDGES. Table 1 shows that the bifurca-
tion load predicted by CLAPP was less than its corresponding set of experi-
mental loads for every specimen. This unexpected behavior can be explained
as follows. Because the radius of a specimen was less than 12.0 in,
25
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Panel Dimensions: 16 in x 16 in2 00O - Fiber Pattern: [0/+45/90] s
Boundary Conditions: Clamped curved edges, Bifurcation atSimply-supported straight edges 8125 lb
IOOO Finite-Difference Grid: 20 x 12 Lost load carry in" o€ ./ capacity 5700 lb
AA
- 00 •i Y
o LOAD IHTETV'i.yf3
400 A
El - numerical200 --- experimental
00 I I I
0 0.5 1.0 1.5 2.0 2.5 3.0AVERAGE END SHORTENING, in x 10-2
FIGURE 10. Numerical and experimental load versus end-shortening curvesfor a 16 in x 16 in panel with simply-supported straightedges.
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4400Buckling Limit When Circumferential .- 31 1 1L,.
4,200 Displacements are Precluded cliverqeuce at 0.01975
On0
3800
3600 Analytical Equilibrium Path,,
3400
3200 - 210 b.b c l(
3000
2800
2600 Bucklinq Limit When-z_ 52 bCircumferential 22 b 0
2400 Displacements Occur -
Freely 11250
2200
2000 0 _,-Experimental EquilIibrium~ Pa-th,
1800
- 1600
0400
1200
10("o PANL; 16 in x 8 in
800 FIBER PATTERN: 10/901EDGE CONDITIONS: Clamped Curved Edges
600 S impl v-supported st ra ighted a s
400
200
0.0 0.,2 0.4~ 0.6 0.3 1.0 1.2 1.14 1.6 1.8 2.0 2.2 ?.4 2.6 2.5 3.0
End-Shn)rtenin 1 (x 10- ) ( inches)
FIGURE I. Analytical and exter imt'ntal loaid vs. end-'.horioni nn cuives for p~iflt' Iwiji h imoily-suippoirtd ',traioht eqs
27
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>L
U- -u C
E W a Q)
:) 'a
7 7p
-L H- wiC
'i:C:
a~ 0
C- L) -
- Lc3
C) C C)
-C: ) ) C: C) C ) C - 0 )0 0 C: ) 0j CD C1 C
N N - CIS C t
C) C '.C H '
28 >
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C:
o
0~
-Cc,
C)D E
01) r-.u
u ~0 4) (
0z n
CIO C)C
CC00
-' C)
j c
IVOON
29
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distortions of the straight edges of a specimen occurred upon clamping
its curved edges in the testing fixture. The experiment buckling load is
believed to correspond to a limit point load that is greater than the
bifurcation load for a perfectly cylindrical geometry. In other words,
the initial distortion of the straight edge- of a specimen prevents an
experimental detection of a bifurcation load corresponding to a wrinkling
of these edges for a perfect cylindrical geometry under a uniformly dis-
tributed edge compression.
We remark that the bifurcation loads predicted by CLAPP correspond to
cylindrical specimens without initial imperfections under forces that are
uniformly distributed along the curved edges. It is important to note
that axial and circumferential dispiacements along the curved edges are
not specified. Consequently, theory predicts a specimen will collapse at
the bifurcation load.
The experimental model is clamped tightly in the head-plate and in the
base-plate so that circumferential displacements along the curved edges are
prevented. More importantly, axial deformations are restricted by the
relative movement of Lhe cross-head and the platten of the testinq machine.
Consequently, when the straight edges buckle the testing fixture prevents
the collapse that theory predicts for the specimen under uniform load. As
a result of the clamp conditions the specimen retains significant load
carrying capacity. In fact, the experimental buckling loads correspond to
limit points in the post buckled region.
A close inspection of the strain data indicates the strain at the
straight edges changed sign at loads that are in the appropriate neighbor-
hoods of the theoretical bifurcation loads. The sign change on the edge
30
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strains corresponds to the observed severe distortion of the straight edges
of a specimen. The load levels at which the sign change occurred depended
on the initial imperfection in the specimen.
CLAPP was modified so that the buckling behavior of specimens under
prescribed uniform end-displacements could be studied.
Figure 14 shows the experimental equilibrium paths for the 16 in. x
8 in. specimens with the [0/90]2s fiber pattern. It also shows equilibrium
paths predicted by CLAPP for initial imperfections of the form W (x,y) =
WI(l+cosrx/2a) for amplitudes WI = 0.0, +0.005, and -0.010. The limit point
buckling loads discussed previously are clearly evident. The ratios of the
experimental buckling loads to the theoretical limit load for a perfectly
cylindrical specimen are 0.85 and 0.83. The ratios of the experimental
buckling loads to the theoretical limit load for an initial imperfection
of amplitude 0.005 are 0.93 and 0.91. Even better agreement is expected
for the exact imperfection distributions.
Figure 15 shows the strain distribution at various load levels for the
specimen discussed in the previous paragraph. Evidently, the force applied
to the curved edges of the specimen was uniform during the early stages of
the loading process; that is, during the initial increments of prescribed
end-displacements. Accordingly, the bifurcation load predicted by CLAPP
for a uniformly applied end-load should agree qualitatively with the load
at which the sign change occurred for the edge strains. The theoretical
bifurcation load from fable 1 is 476 lb and the load at which the axial
edge strain ceased to increase was near 600 lb.
Figure 16 shows the nodal forces predicted by CLAPP for the same speci-
ment distribution. During the initial increments of prescribed end-
31
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0 7
C,
C C
C) co-L C
C)C
- L-) C
LL- L. CC
xo '
w LLJ0 z CL.)0 Lj >> - .s *C~
vi~~- 4)L;)L0
(T\ --4
00
LU a. m
o 00 0 00 00 0 0
(qi) avo ivio
32-
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500 *STRAINI GAGE LOCATION
FINITE-DIFFERENCENODAL POINT
400 -PANEL: 16 in. x 8-i
- (o/9012s
S300- ime
curve edge
200 2
-~jX:I.'0CzL.J H
2.. 34 8 9 i
GAGE LOCATION
FIGURE 15. Experimental strains corresponding to prescribed Values,of end-shor ten ing for test -.pec i ins Wit h LmflSLpporte.I
t ro i (Ilit edge,,.
33
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cc
Cr~l U
cc,-
Z - c c
c C) ) \
LLJ~- -- 0
-IT~' z -o
C3 Co_C ~~~ LuDw-
J)
-vi
CC
AO c
C- 001
C C ,
U
- 0
C-,
0 0 0 3 0 03 0 0 0DLI' n ~ N - 0 C 0) \ Ul -T (N -
(qi) avoi IVOON
314
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displacements the strain distributions and the nodal force distributions
are nearly uniform. These distributions become nonuniform as the loading
process continues; however, there is a visible agreement between the
experimental strain distribution and the calculated nodal load distribution
for all levels of prescribed end-displacements.
(IV-2). ANALYSIS OF RESULTS OF TESTING PROGRAM B. The theoretical buckling
loads shown in column 6 of Table 2 were calculated assuming that each panel
was subjected to prescribed end-displacements that were uniform along the
curved edges. Calculations were made for 16 x 11 and 20 x II finite-
difference grids to check the convergence of the numerical process.
SPECIMENS WITH SIMPLY-SUPPORTED EDGES. The experimental equilibrium paths
for five 16 in. x 12.83 in. specimens with the (0/+45/901 s fiber pattern
and simply-supported straight edges are shown in Figure 17. The load at
which each specimen buckled is marked on the graph beside the corresponding
equilibrium path. The theoretical equilibrium path is also shown in the
same figure for the perfect panel and for an initial imperfection amplitude
of -0.010 in. The two paths essentially coincide except that their termina-
tion points (buckling loads) are different (8064 and 6608 lb. for the per-
fect and imperfect panels, respectively). These buckling loads correspond
to a 16 x 11 finite-difference grid. A 20 x 11 finite-difference grid was
also used to calculate the buckling loads for the same perfect and imperfect
panels. The equilibrium paths in this case were indistinguishable from
those obtained using the 16 x 11 finite-difference grid except that their
termination points (buckling loads) are somewhat less (6950 and 5622 lb.
for the perfect and imperfect panels, respectively) than those associated
with the 16 x 11 finite-difference grid.
35
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Figure 18 shows theoretical equilibrium paths for the perfect panel and
the imperfect panel (WI = -0.010 in.) where, instead of using end-displacement
as a measure of the system displacement, the norm of the transverse displace-
ments is used. These curves exhibit more clearly the nonlinear character of
the equilibrium path. These curves correspond to the 20 x 11 finite-
difference grid. Also note the mathematical form of the geometric initial
imperfection shown on the same figure.
The theoretical buckling load was detected numerically as a change in
the system buckling determinant from positive to negative. This indicates
that the simply-supported panel experienced bifurcation buckling. A plot
of the normalized buckling determinant versus total end load for an initial
imperfection amplitude of -0.010 in. is shown in the upper left hand corner
of Figure 18.
The initial imperfection amplitude corresponds to a radial deviation
from a perfect cylinder of 0.020 inches at the geometric center of the panel,
which is approximately equal to one half the panel thickness. This is a
rather large initial imperfection. The magnitudes of the measured initial
imperfections were frequently larger than 0.020; however, the distribution
of the imperfections were different. Generally, the largest imperfections
occurred near the edges of a specimen with somewhat smaller ones occurring
near the centerline.
The 16 x II and 20 x 11 finite-difference grids gave 8064 lb and 6950
lb as the bifurcation loads for the perfect panel. That is, the 20 x II
grid predicted a bifurcation load 13.8% lower than the 16 x 11 grid. Further
improvement in the theoretical buckling load is expected with a further
refinement in the finite-difference grid. CLAPP is presently dimensioned to
36
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In) In en )
Inn
-~S-
1.0 .0 oC- In O .Cco C0 r-
CD. .0 "a(Zr .0 0: C0
11 S5- '- k.0 LO) 0
-: 00 U
-0 I (j C 0:2cC\J -0 (Nj 4-
S.. - 2 (A:9 I~ CCC -
E- ~Cj CD (= - k C\j ca_
-C L) . ( x LOV) E
Alo U) a ~ -. ~w+Jo .0- D s- - s-
_0~~ c 0cI 'a 0- oo F
-0 4-3 SO.- CL E1x10 ) cCl 0 ) S0 -4- V)- a
*- .. > o U C') LU C)( I. - CL (V-- -
+1 C) :30 EO .. Wc S.. O0) u :3-0 c0O= +)0
x LOJ a)04 L.-L'(V---- c
+i E C. a) G
O o .-
LUJ
F- U CA
0a. LO 4-3 a)03 - 5-..-
C) L C) CL
a- La.. Co L) 1O(.C')
C:)oD 0) 0) CD C0 0) 0 C0 0D 0 00 0 0D 0 0D C0 0D 0 0 0D0D 0) 0 0 0D CD C= C CD 0
0D (n 0; rl: I. ) 1r CO; (N-7
qt 'aVOI OlN] lVioi
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C)
5- - ) EE LnO*I a0) 4-1
LO (J 4- ( UU CL-a)L(L\ s 0 0) V)0 Cr a4)E
ea c. LA >' C4) 0 C -0)
on w 0 :
,n-0" )-C a) 0) I- Q) (N. +-.W )v C: -C~ I I -0 - C) C = C) 0-0' a - C0) 1 If 00 -:T.- ) a C
4)4-) iLA OLLn N O *~-a.'1O 0 CD 0--0I) * v
- = S-
0)4-4- E 0
- C) 0) U
4- S-u- 0M~ < CD U-
CL C:) a) 0L) CL
ULU L.1 U- ( )= C _- .C:< - CD co 4-) -
CL U- wi C) '0S- S-
C) o0+-)4- i
C C=
S-c-
C~ C) 4)0
LO - C) -N a)
-u LJn
* 4-)
a m ro =
-4- CLS
0- C) Ci
oM 0-
09 0 0D C ) C
m ~ ~ o 0;L; 0
qL -IVO 0N IVI>
038
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handle a maximum 20 x 12 finite-difference grid, so that further refine-
ments were not undertaken in this investigation.
The 16 x 11 and 20 x 11 finite-difference grids predicted bifurcation
loads of 6608 and 5622 lb for the imperfect panel (WI - -0.010 in.). Thus,
the 20 x 11 grid predicted a bifurcation load 14.9% lower than the 16 x 11
grid for the imperfect panel. Again, improvement in the theoretical buckling
load for the imperfect panel can be expected for a more refined finite-
difference grid.
Figure 18 shows that the experimental buckling loads are not grossly
misrepresented by the buckling load predicted by the 20 x 11 grid for the
imperfect panel. Based on the buckling load predicted by the 20 x 11 grid
for the perfect panel (6950 Ib) the ratios of the experimental to the theore-
tical buckling load for the five specimens are 0.831, 0.793, 0.741, 0.716,
and 0.668. The last ratio really should not be counted because this speci-
men had been tested previously with very loose straight edges, Based on
the buckling load predicted by 20 x 11 grid for imperfect panel (5622 lb)
these ratios become 1.03, 0.980, 0.918, 0.885, and 0.818.
The theoretical curves, and thus the theoretical buckling loads, upon
which the foregoing ratios are based correspond to simply-supported straight
edges for which circumferential displacements are unrestrained. It is
impossible to be certain of the nature of the boundary condition along the
straight edges of the test specimens. As an example of the uncertainty of
the type of boundary condition that existed along the straight edges of a
test specimen consider the test specimen for which the experimental buckling
load was found to be 5775 lb, the largest of the bucklinq loads of the five
specimens. For this test the shoulders of the vertical pressure blocks
39
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were filed to a rounded configuration so that the blocks contacted the speci-
men along a straight line. In the other tests these contacting surfaces
were flat and tended to bend the panel when the pressure was applied. The
former, it is expected, allowed a more freely occurring rotation at the
edge for which the corresponding buckling load should be expected to be
less than that for the latter case. As can be seen this was not the case.
All this suggests that the edge conditions at the straight edges of the
test panel are uncertain.
It is felt that the conditions along the straight edges of the test
specimens is the principal source of the difference exhibited between the
experimental and theoretical buckling loads. It is also felt the CLAPP is
much less at fault for the difference referred to.
It should also be noted that any pressure exerted by the vertical pres-
sure blocks on the panel tends to retard the free occurrence of axial dis-
placements along the straight edges. This could give rise to shearing
stresses in the panel which would lead to lower axial buckling loads.
Finally, the clamping mechanism prevents circumferential displacements from
occurring freely along the curved edges. This could cause local distortions
near the curved edges that could lead to lower buckling loads. The model
for which the theoretical buckling loads were computed assumed that axial
displacements along the straight edges and circumferential displacements along
the curved edges are unimpeded.
SPECIMENS WITH UNSUPPORTED STRAIGHT EDGES. The experimental equilibrium
paths for six 16 in. x 12.83 in. specimei. with the [0/9012s fiber pattern
and unsupported straight edges are shown in Figure 19. The load at which
each specimen buckled is marked on the graph beside the corresponding
40
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equilibrium path. The theoretical equilibrium path is also shown in the
same figure for initial imperfection amplitudes of -0.0025 and -0.005. As
was the case for specimens with simply-supported straight edges, the theore-
tical equilibrium paths for the 16 x 11 finite-difference qrid essentially
coincide for initial imperfection amplitudes of -0.0025, -0.0050, and -0.010
in. Moreover, the buckling loads corresponding to these iniitial imperfec-
tion amplitudes differed only slightly, as can be seen from Figure 20.
The equilibrium path corresponding to a 20 x 11 f.inite-difference grid
differs only slightly from that corresponding to a 16 x H1 grid. The
buckling loads for the 16 x 11 and 20 x 1) grids for an initial imperfec-
tion amplitude of -0.01 in. are 3416 and 3320 lb, respectively. In this
case the refined finite-difference grid did not influence the buckling load
nearly as much as it influenced the buckling loads for the simply-supported
panel.
The experimental equilibrium paths depicted in Figure 19 indicate that
the stiffness of each test specimen changes noticeably in the load range
400-1000 lb. This change in stiffness coincides also with the observed
reversal of the axial strains at the straight edges of the test specimens.
Consequently, it is believed that this change in stiffness signifies the
load-level at which the straight edges of a specimen lost their capahility
to resist greater axial loads.
The theoretical equilibrium paths shown in Figure 20 for various initial
imperfection amplitudes reveal that a bifurcation occurs at approximately
1134 lb for a perfect panel This agrees well with the experimental loads
corresponding to the changes in stiffness of the test specimens as shown
in Figure 19.
41
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Using the limit load (3320 ib) corresponding to an initial imperfection
amplitude of -0.010 and the 20 x 11 finite-difference grid, the ratios of
the experimental limit load to the theoretical limit load are 0.818, 0.753,
0.741, 0.693, and 0.652. The theoretical limit load used to calculate
these ratios are based on an axially symmetric distribution of initial
imperfections (W° = WI (l+cosnF/a)). The actual distributions of initial
imperfections indicated a pronounced distortion of the straight edges of
the general shape represented by the mathematical equation expressed above,
that dimenished as the specimen centerline was approached. Actually the
center region of the test specimens were relatively straight in comparison
to the straight edges. This observation is revealed by the imperfection
data listed in Appendix C.
The equilibrium path for an initial imperfection distribution given by
W = WI (l+cosns /a) (n/b) is shown in Figure 20. This distribution more
closely represents the actual imperfection distributions. This equilibrium
path coincided with the other paths shown in Figure 20. The limit point load
for this imperfection was 3460 lb. which is essentially the same as the limit
point loads for the other initial imperfections.
42
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3400
3200 - 3416 lb 16x1l grid, WI -0.010 in-
Theoretical 3320 lb 20xll grid, WI -0.010 in3000 equilibrium paths /
for WI = -0.0025 and
-0.0050 in.2800
2600
2715 lb
2400 -
2500 lb
2200 -2460 lb
2300 lb
2000 2165 lb
S 1800
S 1600
U-i_j 1400 -~ Experimental equilibrium paths
1200
1000 PANEL 16 in x 12.83 in.
FIBER PATTERN: [0/90]2s
800 / BOUNDARY Clamped curved edges,-CONDITIONS : unsupported straight
edges600
400
300 - w° = WI (1 + cos x/a)
200
0 25 50 75 100 125 150 175 200
END SHORTENING, x 10" in.
Figure 19. Theoretical and experimental equilibrium paths for specimens
of Program B with unsupported straight edges.
43
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f I ~Ln- a)
LUj C-0 -
C LUJ 4-)
CC:)LUJ -: -
cr cl L LU
%D CD c
.- -D C) 0)I~ UL 0 - 4-'
c - : 0l - ) L
LL- o - CD +
.0ia C J ) c 9 iI
S- - 2-- C D71 WMI LU U- < M) 0V
CA a.C CL LL- -L C O
.- LI) >)(90
S- Lo C) )CD C~ C) C-). ( 100)
C.. CD C) II
.4-'C 4- 4-~C a .
0~( 04 m. (m C\ - U-
oZ C L0
C- n (~C) -0
0)~~C CM In ( >
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CD9( ( C) 0 C) C-) ) CC:)~~C'H U' D L -) " Z
cl0(9 aj44
if if f IS:3
IqL SVIO3 ~
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SECTION V
LONGITUDINAL STIFFENERS
(V-1). INTRODUCTION. The compute- program CLAPP was modified to include
the effect of longitudinal stiffeners on the buckling behavior of fiber-
reinforced panels by adding the total potential energy of the stiffeners
to the total potential energy of the panel. Accordingly, the total poten-
tial energy of a stiffener element is developed in this section.
The stiffeners considered in this section have thin-wall open cross
sections and are assumed to coincide with the finite difference grid lines
that are parallel to the generators of the panel. It is not necessary
that a stiffener be associated with every finite difference grid line.
A stiffener is assumed to be made from an homogeneous isotropic mater-
ial; however, the developments remain valid for quasi-isotropic, fiber-
reinforced stiffeners. The special properties of quasi-isotropic, fiber-
reinforced stiffeners are described later. It is further assumed that
the cross section of a stiffener does not vary along its length, and that
each stiffener is free of externally applied forces.
Each stiffener is assumed to be rigidly attached to the panel along a
finite-difference grid line. A point of attachment is defined as the
point on the reference surface of the panel that lies on the normal throug '
the centroid of the stiffener cross section. Mathematically, the displace-
ment components associated with the panel and the displacement components
associated with the stiffener are required to be continuous along this
contact line.
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(V-2). STIFFENER STRAIN ENERGY. An expression for the strain energy asso-
ciated with small displacements of straight beams with thin-wall, open cross
sections is given by Bleich and Bleich [41
2 ~ 2 2U =2 E s + +JG(') + EA()+ dz (V-l)Sf ; S C
The quantities appearing in Eq. (V-1) are defined as follows. The rectangu-
lar coordinates ; and n coincide with the principal centroidal axes of
inertia, and z signifies a coordinate measured along the centroidal axis of
the beam. Thus, I,., and I are principal centroidal moments of inertia,
A denotes the cross sectional area, J is the torsional constant, and 7 is
the warping coefficient for the cross section. Young's modulus and the
shearing modulus are denoted by E and G, respectively. Finally, U and V
are components of displacement of the shear center parallel to the and n
axes, respectively, W is the axial displacement of the centroid of thec
cross section, andA3 is the unit angle of twist that the section experiences.
The first two terms in Eq. (V-l) represent strain energy due to bending'
about the principal axes of inertia, while the next two terms represent
strain energy caused by twisting and axial deformation, respectively. The
last term represents strain energy associated with warping of the cross
section. The strain energy associated with warping is usually discarded in
stiffener analyses; it is also discarded in the present analysis.
Since it is assumed that every stiffener is free of externally applied
forces, Eq. (V-1) also represents the total potential energy of a stiffener.
Energy methods have been employed by several investigators to examine
the effect of stiffeners on the buckling behavior of plates and panels.
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These investigators do not agree universally on the terms that need to be
retained in the stiffener energy expression. Donnell [51 discards the
strain energies associated with axial deformations and bending about an
axis perpendicular to the reference surface of the panel. Thus Donnell
assumes that the dominant actions of a stiffener are bending about an axis
parallel to a circumferential tangent, and twisting. Szilard [6] adopts
the same reasoning, but argues that strain energy due to twisting can be
discarded for closely spaced stiffeners. Palamarchuk and Polyakov [7]
retain the same bending and twisting energies, but include terms that
represent the effects of externally applied forces and initial geometric
imperfections.
The investigations cited consider only stiffeners with symmetrical
cross sections. Stiffeners with unsymmetrical cross sections are treated
in the present developments.
(V-3). STIFFENER ENERGY IN MATRIX FORM. The total potential energy for a
stiffener can be expressed in matrix form as
El 0 0 0 U"
0 E 0 0 V1
V = [ v', ', w dz (v-2)0 0 JG 0 IB'
0
0 0 O EA wC
As was stated previously, U and V are components of displacement of the5 5
shear center along the t and n axes, w is the axial displacement of thec
centroid, and 2 is the rotation of the cross section per unit length.
Connectivity of a stiffener to the panel is accomplished by expressing
these displacement variables in terms of the displacements (UD ' V D ) of the
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point of contact of a stiffener
with the panel. The situation
is depicted in Figure 21.
It is shown in Ref. [41 that, x
for small displacements, the dis-
placement components for a generic
point in the rigid cross section
of a stiffener are I / .-
FIGURE 21. General thin-wall openU =U + (n scross section.
(v-3)
v = V - )
At the contact point D, Fi, =D and j =
TD' so that, with the aid of Eqs.
(V-3),
U s 1 0 - (n s -j D U UD
V = 0 V (V-4)
S0 0 1 1
Because plane sections remain plane (r = 0) the axial displacement of
the contact point, wD1 is
wD = w - F r D V (V-5)D c D c 9 c
where uc and vc are centroidal displacements along the t and n axes as
shown in Figure (21), and ( )' indicates differentiation with respect to
z. From Eq. (V-3),
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U = Us + n IL (v-6)
V =V - nlVC VS S
so that Eq. (V-5) becomes
= w - F lDVn (V-7)wD = W D U - D VD ( -7
Eqs. (V-4) and (V-5) lead to the following transformation
Uls 1 0 -(n -n) 0 l
v,, o ooVl01 0 0 21s D DD (V-8)
1 0 0 1 0 0 So
B' 0 0 0 1 0]CL D nD [W0I
Eq. (V-8) permits the strain energy of a stiffener to be expressed in terms
of the displacements experienced by the point of contact of a stiffener
with the panel.
(V-4). DISPLACEMENT CONTINUITY. To enforce the required displacement con-
tinuity along the line of contact of a stiffener with the panel, it is
necessary to project the displaceme,. vector of the contact point along the
circumferential tangent and along a normal to the panel. According to
Figure 21,
UDi VCosat sinciUcos n= U (V-9)
viD I-sina cosa n
where Ut and Vn are the circumferential and normal components of displace-
ment of the contact point D.
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Accordingly, the contact point displacement vector appearing on the
right-hand side of Eq. (V-S) is expressed as
Ul cosct s i nc 0 0 0 UID t
Vo -sint cosa 0 0 0 U"D n
B" 0 0 1 0 0 B" (V-10)
(' 0 0 0 1 0 a'
!w; 0 0 0 0 I
The assumption is made that the panel thickness is small compared to
the dimensions of a stiffener normal to the panel. This permits the con-
tact point D to lie in the reference surface of the pancl.
Continuity of the displacements associated with the contact point on
the stiffener and the displacements associated with the contact point on
the panel requires that
U =V, B=Wt ,y
U =W, 3'=W , (V-Il)n , yx
wD U, B" = WWDUB ,yxx
Here U, V, W are the displacement components of a point on the reference
surface of the panel.
Eqs. (V-2), (V-8), (V-10), and (V-11) yield the following matrix formu-
lation for the strain energy of a stiffener:
V [d]T[A]T[B]T[S)[B][A)[d] dz, (V-12)
0
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where
[A] = cosa sinca 0 0 1-s i nc Cosc 0 0
0 0 1 0 0 (V-13)
0 0 0 ! 0
0 0 0 0 I
[B] I 0 0
0 1 S D 0 0(V-14)
0 0 0 1
L D 11 D 0I_
[S] El 1, 0 0 0
0 El r "" (V-15)
0 0 JG 0 1
0 0 0 EA]
and
(d]T (V W W W U I (V-16a)
,xx ,xx ,xxy , xy X
To interface with the computer program CLAPP, the elements of the
stiffener displacement vector [d] are rearranged so that
T[d] T [U , V , W , W , W I (V-16b),x , X XX ,x X~ ,xy
The total potential energy of a stiffener becomes
V = J [dIT [PAS2] [d] dz (V-17)
0
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The matrix [PAS2) results from carrying out the operations indicated in
Eq. (V-12) taking into account the alterations of the matrices [A], [B],
and [S] because of the rearrangement of the elements in the [d] matrix.
The elements of [PAS2] are given in Figure 22.
A final transformation is required to express the total potential
energy in terms of the finite-difference grid point displacements.
(V-5). FINITE-DIFFERENCE CONSIDERATIONS. The strain energy density of
a stiffener element is assumed to be constant over the length of the
element. Moreover, the strain energy density is assumed to be equal to
its values at the midpoint of the element length. Consequently, the total
potential energy for a stiffener-element is taken as the product of the
strain energy density at the midlength of the element and the length of
the element. Symbolically,
V = [d T[PAS2][d] x (V-18)e
where [d] is the displacement vector associated with the midpoint of the
stiffener-element.
Nine different stiffener-elements are required. These stiffener-
elements correspond to the nine types of area-elements used in CLAPP, one
interior stiffener-element, four boundary stiffener-elements, and four
corner stiffener-elements. The nine stiffener-elements are shown in
Figure 23, which also shows the stiffener-element orientation and midpoint
along with the local numbering system for the surrounding finite-difference
grid points.
For each stiffener-element the midpoint displacement vector (Eq. (V-16b))
is transformed to the local grid point displacement vector
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CD CD C) C)
6 66 6 r_ (A
tU a 0
0 0- 0 0
C. kPC, LP
I a + +
mn Ln0o) 6 u Z
0 ) (N (n kP 0
+ 6 n 0 -. -6 (An - 0 U LiiL nrC 0 L) a 04(
u U N + .~-- CD an- a C a 6 m 0 U
a) LLI m Wn m Vn N' klP C3 XIP- X 0 'J CL r_- 5= - C-
n ~ (\ .- < in cc 01ccP C.- <~ 0m i~ n uiJ I~P LIi r-
1 Lii Lo. LIi
<C + I + I Lii Csj
LCL.
3X
an P C, u C a)
C L 6 0 C)
a* a anC, -06 0 CM )
o -6 l 0 o CA 0LA - 0 C-
0z 0 gr Nu. U Cz < 03 Gi
w UP~ Lii _rC 4-'
- + a I ILL) Lii La-
C4a)
S.-
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o-Tc -' ar\ an -
Q) E)
L. C
u. tA w 0I- (
C "- E L
c - a- :3.-w
L. Q 0)-0Q) r-C. E.CLA 0 L- Q)
IN ~ ~ ~ a C:0- ~ .C)C(U -C U~) (DE
E -3
r-.m Q) c. C)
S-u Cl w'
(a 4.C .0
=) .- 00V0)
C)Q n* C.
I- 0 -' I\ '.
(~ 0 0 -0 e~ C
a)0
C)0
C )L
(V c
0 0 )
u i0) >-v
co C>- 00 -M 0 0 ,
r44
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T
[q] = (Wi , UI , V1 W 2 U 2 , V2 . W9 U9 , V9 ] (V-19)
through the relations
d. = c.j q. (V-20)i j IJ j
where the matrix [C] is composed of coefficients that depend on the vari-
able spacing of the finite-difference grid. Accordingly, the total poten-
tial energy for a stiffener-element is
V T [CTVe = 2 [q] [c] [PAS2][C][q] Z (V-21)
The transformation matrix [C] depends on the location of the stiffener-
element in the global system. To illustrate the procedure used to estab-
lish these matrices, the transformation matrix for the interior stiffener-
element shown in Figure 24 is derived.
In the longitudinal direction, the midpoint (subsequently referred to
as the stiffener-element centroid) of the stiffener-element contains the
centroid of the corresponding area-element. This follows from the defini-
tions of an area-element and of a stiffener-element. The corners of an
area-element are the centroids of the areas contained between adjacent
grid lines. The length of the corresponding stiffener-element is equal to
the dimension of the area-element parallel to the generator of the panel.
A derivative of a centroidal displacement with respect to the lonqitu-
dinal direction x, denoted by ( )', can be expressed as a linear combina-
tion of displacements at the three finite-difference grid points (i-1, i,
i+l) lying on the longitudinal grid line.
A general one-dimensional centroidal function, f, and its derivatives
are expressed as linear combinations of the function values at the three
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0
E
.7# 4, j+l
centroid M
3 2longitudinal
h k direction
6 29
• -- h ' = k
i- i+l
FiGURE 24. interior stiffener-element with qrid spacinq
and grid line notations.
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node points on the jth grid line as
f (k-h) (3h+k) f + (h+3k) (3h+k) f (k-h) (3k+h)i 6k(h+k) i+l 16hk i 16h(h+k) i-l'
f, L f + (L L) f + - (V-23)i 2k i+l 2h 2k 2h i-V
and
f,. 2 f f + 2 (V-24)k(h+k) i+l hk i h(h+k) i-
where h and k are longitudinal spacings between the grid lines i-l and
i, and i and i+l, respectively.
A derivative of a centroidal displacement with respect to the circum-
ferential coordinate y, denoted by C ), can also be expressed as a linear
combination of displacements at suitable finite-difference grid points by
means of a Taylor series. Accordingly, a Taylor series expansion about
the point (i, j) yields the two linear equations
fj+l = f " + m f. + m2 f. (V-25)
and
fj i = f " - Q f. + Z2 f., (V-26)j- j JJ
where Q. and m are spacings between the j-1 and j, and j and j+l circumfer-
ential grid lines. Eqs. (V-25) and (V-26) lead to the first-order central
difference formulas
Sf (.-m)f m (V-27j M(P+m) j+l Zm j P. f+M) i-I
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and
". 2 2 f + 2 (V-28)j m(+m) j+1 -m j (M+ fj
The centroidal displacement vector [d] includes mixed derivatives also.
The coefficients in the transformation matrix [C] that correspond to deri-
vatives with respect to x are obtained from Eqs. (V-23) and (V-24) for an
interior stiffener-element. The coefficients in the transformation matrix
[C] corresponding to the mixed derivatives are determined by appropriate
combinations of Eqs. (V-23), (V-24), and (V-26).
A general two-dimensional centroidal function, g, has the mixed deri-
vative
I + (V-29)2 =k gi+l 2h 2k i gi-l"
Using Eq. (V-26) yields
I, z O(-m) mg= 1 ___ tm - m(v-3o)2k m( +m) gi+l, j+l Zm gi+l, j 7m gi+l, j+(3l
1 - 1 _ 9. (-m) - m (V-31)
2h 2k m(9+m) gi, j+l Zm i, i z gi, i
+ z (Z-M) - m (V-32)
2h inF+m- g-I j+ I in gi-l, j -m gi-], j- I
Identification of the nine surrounding grid points with the local num-
ber system determines the coefficients in the transformation
g =ci gi i = 1, 2,... 9. (V-33)
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The coefficients for the mixed derivative g" are obtained in a similar
manner.
The total potential energy for any stiffener-element is expressei ai
V [q) T [CAS2][q] x . (V-e
where
[CAS2] = (C]T [PAS2] [C] V-35)
Eq. (V-34) is the formulation of the total potential energy for any
stiffener-element that interfaces consistently with the area-elements used
in CLAPP.
(V-6). INCORPORATION INTO CLAPP. The incorporation of lonaitudinal stiffe-
ners in the computer program CLAPP is accomplished with three subroutines.
The first of these three stiffener subroutines is named SCOEF. SCOEF
calculates the elements of the matrix [PAS2]. Since [PAS21 depends only on
the material and geometric properties of the stiffener cross section it is
calculated once for each element and stored.
SCOEF permits the user to select any of seven stiffener cross sections.
It also provides for any other cross section through a user's choice ontion.
For the various stiffener cross sections included in SCOEF see the user's
manual in APPENDIX D.
The second stiffener subroutine is named STFDIF. It calculate, the
elements of the transformation matrix [C] of Eq (V-20). The subroutine
FDIFF of CLAPP performs similar calculations for each area-element. Con-
sequently, when FDIFF is called to calculate [C] for an area-element
STFDIF is subsequently called from FDIFF to calculate [C] for the corres-
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ponding stiffener element.
The third stiffener subroutine is named ATBAS. It performs the matrix
multiplications indicated in Eq (V-35). This subroutine is called from
the subroutine STFDIF. ATBAS has been constructed to take advantage of
the numerous zeros that occur in the matrix [C].
The main program and the subroutine FDIFF of CLAPP are modified so
that longitudinal stiffeners can be included when appropriate. Additions
to the main program read in stiffener indices indicating (a) that stiffe-
ners are to be included, (b) the choice stiffener cross section, (c) whether
stiffeners are located on the inside or outside of the panel, and (d) if
stiffeners occur on every finite-difference grid line. The main program
calls SCOEFF to construct the matrix [PAS2]. The additions to the subrou-
tine FDIFF determine when the stiffener energy is required in an analysis
that does not include stiffeners at every grid line. When it is appropriate,
STFDIF is called to calculate the stiffener-element energy which is imme-
diately added to the correspoinding area-element energy. The procedure
used by CLAPP to assemble the -,ystem stiffness matrix for area-elements
proceeds in precisely the sa.e manner when stiffeners are present.
(v-7). QUASI-ISOrROPIC FIBER-REINFORCED STIFFENERS. A strain energy
expression for a quasi-isotropic, fiber-reinforced stiffener that is ana-
logus to the strain energy expression for an isotropic stiffener is estab-
lished in this section. For the purpose of the present development a
quasi-isotropic material is defined as one possessing midplane symmetry
and alternate zero and 90 degree fiber directions. Thus, for a stiffener,
the zero fiber direction is assumed to coincide with the longitudinal axis
of the stiffener, and the 90 degree fiber direction is perpendicular to
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this axis.
The stress-strain relations [2] for a general fiber-reinforced laminate
are
N All A1 2 A 1 6 e BIl B1 2 B 1 6 Kx lx 3 x
N = A 1 2 A 2 2 A 2 6 e + B12 B2 2 B2 6 K (V-36)
N A 1 6 A 2 6 A 6 6 2e B16 B26 B6 6 2K
M B11 B12 B16 e DI, D12 D16 K
My B12 B2 2 B2 6 e + D12 D22 D26 K (V-37)y y y
M B16 B26 B6 6 2e D16 D26 D66 2Kxy xy xy
Formulas connecting the elements of the laminate stiffness matrices [A],
[B], and [0 with the material properties and the geometric locations of the
individual layers are
A. Qijk - (V-38)B k=l (h k-IV
tj 2 k ij k k-
N
D.. = Z (h3 - h3 ) (i,j = 1, 6). (V-40)iJ k=l ij k k-I
Pertinent geometric quantities appearing in these relations are defined in
Figure 25.
The laminate is assumed to possess midplane symmetry so that the B..
are identically zero in Eqs. (V-36) and (V-37). It is also assumed that
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the stiffener experiences a membrane state of stress like the one shown
in Figure 26. Consequently, the dominant bendi g action results from the
moment caused by the membrane force Nx
If the cross section of a stiffener is assumed to be rigid, then e = 0y
so that
N = A l l ex + A1 (2e xy) (V-41)
and
N = A1 6 e + A6 6 (2e ) (V-42)xy x xy
Now A1 6 0 because of the laminate fiber directions are either parallel
or perpendicular to the longitudinal axis of the stiffener. Consequently,
the stress-strain relations appropriate to an analysis of fiber-reinforced
stiffeners under the foregoing restrictions are
N = All e (V-43)x x
and
N A66 (2e ). (V-44)xy xy
These relations are analogous to the isotropic stress-strain relations
used by Bleich and Bleich [4] to arrive at their expression for the strain
energy of stiffeners made from isotropic materials. All that is required
to make the isotropic strain energy expression valid for quasi-isotropic
stiffeners is to appropriately identify E and G of the isotropic case with
All and A6 6 for the quasi-isotropic case.
To do this, consider that
62
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K z& layer
aer number1
FIGUR 2a5e Cros_ sec ionfla inat
FIGURE 25. Cers secton of litre ,,fraifnr
S6
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N N
N -k N kAll = E --0. 1 (h k -hEk ) t z (V45k=l k=l
and
N N-k -A6 6
= Z --066k (hk - hkl) = t Z (V-46)
k=l k=l
if the thickness of each layer is the same.
The subscript k signifies that the k-th layer is under consideration.
The Qij are symmetrical and are the material coefficients referred to a
generic set of axis. They are expressed in terms of the material coeffi-
cients, Qij, associated with the material axes of a layer through the trans-
formation:
Q1,I = Qlcos" 0 + 2 (Q12 + 2 Q66) sin2 0 cos 2 0 + Q2 2 sink 0,
Q12 = (QIl + Q22 - 4 Q66) sin 2 a cos2 6 + 012 (sink e + cos 4 e),
Q22 = Qll sink 0 + 2(Q12 + 2 Q6 6) sin2 0 cos 2 0 + Q2 2 cos4 e, (V-47)
16 = (Qii- Q12 - 2 Q66 ) sin 0 cos3 0 + (Q12 - Q22 + 2 Q66) sin 3 e cos 0,
Q26 = (Ql Q - 2 Q66) sin3 0 cos + + (Q12 - Q2 2 + 2 Q66 ) sin 0 cos
3 ,
Q66 = (Qil + Q22- 2 Q12 - 2 Q66) sin 2 6 cos 2 0 + Q66(sin 4 0 + cos4 .).
The quantities Q are related to the enqineerinq material constants
through the relations:
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E11
lv2v,,1
v-2 Ell v2 1 E2 2
Q12 = Q21 = v 1 2v 2 1 - V1 2 2 1 (v-48)
E22
Q22 = )-v 1 2 v 2 1
Q66 = G12 .
Ell, E22 are Young's modulii of elasticity parallel and perpendicular to
the fiber direction, respectively; G12 is the shearing modulus of elasti-
city associated with the directions parallel and perpendicular to the fiber
direction; and v12, v2 1 are Poisson ratios. v12 is associated with a
strain in the ]-direction due to a stress in the 2-direction and v2] is
associated with a strain in the 2-direction due to a stress in the 1-
direction. It is convenient to let the ]-direction coincide with the
fiber direction.
From Eqs. (V-47) and (V-48)
k Ell
= j = 12"2 for fibers parallel to the stiffener axis
Qk= (V-49)
k E22
Q2 2k = for fibers perpendicular to the stiffener]-12V21 axis
and
Ak
Q66= Q66= G12 (V-50)
for either fiber direction.
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If N is the number of layers in the laminate, then from Eqs. (V-44)
and (V-49)
Nt E l + E22 Ell - E22
A1 ll -V12 V21 2 (V-51)
where
0 if N is evenx= (V-52)
I if N is odd.
Note that when N is odd, the middle or odd layer is assumed to be parallel
to the stiffener axis. If the middle or odd layer is perpendicular to the
stiffener axis Ell and E22 interchange positions in Eq (V-51).
Finrily,
A6 6 = Nt G 12 (V-53)
for N even or odd. Notice that Nt is the total thickness of the laminate
from which the stiffener is constructed.
Now if E and G in the isotropic strain energy expression for thin-wall
open sections is replaced with
All Ell + E22 Ell - E22E Nt 2 + A( 2N ) (V-54)
and
A66= G12, (Y-55)
one arrives at a strain energy expression for the quasi-isotropic material
considered in this section.
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REFERENCES
I. Bauld, Nelson R., and Satymurthy, Kailassam, Collapse I Analysisfor Plates and Panels, AFFDL-TR-79-3038, Air Force Fliq DynamicsLaboratory, Air Force Wright Aeronautical Laboratories, Air ForceSystems Command, Wright-Patterson Air Force Base, Ohio, May, 1979.
2. Jones, Robert M., Mechanics of Composite Materials, McGraw-Hill,1975.
3. Wilkins, D. J., "Compression Buckling Tests of Laminated Graphite-Epoxy Curved Panels," AIAA Journal, Vol. 13, No. 4, April, 1975.
4. Bleich, F., Buckling Strength of Metal Structures, H. H. Bleich, Ed.,
New York: McGraw-Hill, 107-116, 1952.
5. Donnell, L. H., Beams, Plates, and Shells, McGraw-Hill, 204-209, 216-218, 1976.
6. Szilard, R., Theory and Analysis of Plates: Classical and NumericalMethods, Prentice-Hall, Inc., 540-547, 1974.
7. Palamarchuk, V. G., and Polyakov, P. S., "Rational Stringer Reinforce-ment of a Shell with Initial Deflections," Soviet Applied Mechanics,Vol. 12, No. 3, 229-234, 1976.
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APPENDIX A
STRAIN, END-SHORTENING, AND IMPERFECTION MEASUREMENTS FORTEST PANELS WITH SIMPLY-SUPPORTED STRAIGHT EDGES
CLAMPED CURVED EDGES
TESTING PROGRAM A
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C14 en_-a UNT
E c. .u- L C14 - T L r
CD~~ '.0.0 a'o C1 LT+ -7 U\ r olo(1
I- C,4 - LA U.\ C -I 0 LA CO r OD LA' :r r ) C'00 -f' C', m~ -I _:r _:O -.3 LA O\
uj ~I r- C -\D mN C4, (N \ (N \ .' r-I'LN a
IDLrLr 0 C M OU\ r- 0A. m UO % co CD 0 I- -C (N (.7 LA m- -T LA L-. 0 I'). UL\ '. \.1 0 '.
Cl
'0 0 N- (N ' rn-T \.O - LA c0 \-r. ~ 7 0 .f LA)LN- LO V)- O ~ O - L N- ~L O 0 N
'0 N I- C
C: )
IQAL)
IA -N I- m0.T - 0
a- (DO 00=--T LA a) PC C00 0 0 0 0 0000wa)aa\ 0 0 0 C c
(30 cc-~
0 ,D 0 COO , (N N- -'0-3 LA'\ 0 z . COC ON -N
0C :3 -7 00 r\ C 7 U\ 0 N - CO -T0 - (N &)' r, LA 0 N- M~ 0 -T 0a. C-4 COC (N\-t . r- -
U- CYC
c~ z
'0- '0u'- ~ ~ ~ ~ ~ ~ ~ .(N -70 L' -N -C O)0 0 0 0
Z ) M (N) (N C N r , (' LA 'N LA '0 '0 ' D N -N- N-
uj~~~~~~~- M T UN of-m m m
0- (N +1 (N (' ' A A L . 0 - N - N
C Z
C) CD CD (D -> C)- Coc 0 0 LNCD 0 a
.4 m IA
0 -c, C: r r , 0 N Nr
w 0) 0- C > 0'0 0C -- 0 C.) LA C N 0~ (N A (N ' D0 (~ 0 CD 0 0' V)
C> (N 0 Ar C) LA '0 '. 0 Ln CO U"\ 0- Cr - - (N IQI c, ', 0
10 C14 LAO I-a" U\ 0 r LU*\ ~ ~ ~ ~ ~ ~ ~ ~ ~ ( C4 C C' " \- -r-l Z f r
-7 C 69
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EOL Co '. ' Ln '.D m' N '
Z ~ 0 cCO 0 - ' Ln F- CD -T
Qi)
C3 \,D'0 O' -T LA' LAO 0 rr
0~ ~ o. ,N 0 \ 0 u-, L(n O -, C) CD0 0 C-4 N
~~N'0 0 -40 r- x - 0 0\ "~ Nrr~LN N . 0- r- - r- CO 00 L
4.n --c
Cc 00 ) CDC 00 CO 00 NI 04
x( m0'0 C - N N c. 'D0 LA r-
I C-
000 0 . 0 0 0 0 0 r)
N -) c-N. . . . Ci CI C4C
a'~~~ CDOO 0) - 0 N (D- r' 0r C O U\
0 0 00 0 0 0 0 010 0 "A00 0 0 0 " 0 T 0" 10 0 N
~-T LA\ n LA\ ULA U\ Lr\ Lr\ Lr LA\ LA
m' en u- c,4 N o. L\ Lr\ 'L. u\ 0 ""I u-\ -TLn 'D0 \ CO C ~ ' 0 N- 0"% 0 N, C, ff" LA\
.0 0 00C 0 - M -T 0 LA\ CO L\-T LA'0 '0E '0m C ' CO ('0 CO - -T 00 -T co
W 0 N r- N C CO ON m- O\ 0O\ 0 0 - -
z
C) C O 'D Co mO CO t-C O O C ,
4-,
In
Li
o I -0 -0 -m -, LA a LALAILALA'C 0 '0 '0 '0 'I.,3
I 0 -o L
< )L OLA 0000 LA COLA U\ LA 0
0-70
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C 0 O'\ C) r- (N M0 C CO r - . o, , m m C) f.'I '0 mLA 4 Ln c LA N C)LA -T r- (N r- C) (n r Ln (N 00 CD - I'D
-- C14 c(N m' (\ ~ -T LAN LA LrN LA L LA '.0 '. 'o0 '0
2
M T~OL C) ) C m ~ 0 Mm r- 0 Ln -'T " AC C )r- 'c' .) ( A ' 0 ,O% CD (N .0 01) - 0. -T c* L.A LA\ 1- - (N- N( N (N4 m fn -T _z0 UL\ 100 '.0 (N (N
ro0)C N L -Z '.0 CD '.0 C) U-\ (N 00 mNf LA\ cr LA\ 00 - C)
m, ~~\' LA\ - '.D - -T 00 (N '.0 m -7 (N C) m LAr co m, -:I(u - N 0N M M rn -:1-~ -7 LA\ ULA '0 ' '0 '0 (N (Nco
(D m CA ( C) CO cc C\01 -T r-- (N -- CO ;3 CO LA\ f- CA, f(N Lf\C14 -T r- CD -r rN- -T~ CO C14 rN- LA\ CO\ fA (N - Lr\ 0'\ (N UL\
C C1 C- en _4 I -T I I I I I I ID In ID II I
IC)
Ifl ) C)C (N 0O C Lr. C) (N C) C) C) C) CD C) C C) C) C) c. C) C) (1)
0) s- - (N - L AA( LA CAN ..Z LA CA- AL C Ar.LAL \- 0 0~ QY m (N( C)CA( T. LC\ L'\ Lr\ '0 '.0 r (N CO) u
mO L Ln.
CL
C)C C) C) C) 0)C )C C CC) C) C) D C) CC CC) C CD CD
LAjLA, C) LA C C LA\ C) LA\ C) LA\ CD LA\ CD Ul\ C) L\ C) U\ C) LN LA
LA (N W, C) CN "A -- \ '0 -0 C)\ CO '0 (N1 m0 )C N( .CN ~ ~ .CC) (N en MN I -:-U
C - (N CA\ C A)'0 (N( No N(L '0, -0 -- j co m 1 N0 (N (NI Cn- (Nm
m0U m -T -4 U* n 1 - ro- '-
E CD -:3 r- 00C CO - CO CA' -'0 r- co
"- '0t 'T :0 (N -) MO (N, (N - NC
0 ~ - C\c " - m--.r ' - I(D C( C,4 -0 MO '0 I" (N CO . D '0 (N C ( C) 1 (n O-(
U-\ LA O\' -r (N - L U\ r- -T (N C) (N -T LA\ ' WO MS(1( C14 mA m -7 -7 _ LA\ LA\ LA LA\ LA LA LA\
~ ))C) '0 r, -' 0AC CD (N4 MA' - 'D LA 'D0 -7(N CO '0 -T mA (N-' C) LAo0 A LA 9% m(% N C4- '0 mO
(Ui - l (NC nC- - 3 LA LAl LA% '0 '0 (N (N 00 CO CO CO
- CI'. CO LA mAC C) O C) M - r- C0O' C4 (N CO L \ LA L'0 CAN C '0 CO - " CA' m - CA-\'o mO mA C) " M:
- CN N 4 C14 C14 CA. .C) l m -T _:r -T LA '0 '0 '0 '0
C)C C) CD LA ) C) C) LA\ C) C) LA LA LA C) LA LA\ C)
-C) (N .-I CO -:T C) CA C) - ( C) '10 CA CO CA - CO
.- 0N lzA CA% - LA\ LA '0 '0 (N- CO 00 M C(N (NN Z)- CC - - o
0-)
(U LA C)C)OC) ) LAC) L C) LA Q) LA\ C) LA\ C) LA C) C C) (NxO LAO LA C) (N4 LA (N CN Ln r-N C4 (N \ LA (N OC
-~~3 - N( ( NC C ACA. r -- -T -'r LA\ LA LA,\
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IMPERFECTION MEASUREMENTS
(x io-3 in)
BCP 9824-A-2-1 CS BCP 9824-A-2-2 CS
-6 -6 -5 0 -6 -2 -6 -4 -7 -4 !-4 0 -3 -3 -13-14
-6 -5 -3 2 -5 2 -5 -2 7 -6 -3 0 -5' -1 -15 -15
-6 -6 -5 1 -8 0 -6 -3 i -7 -9 -4 -2 -6 -2 -17 -13
-7 -6 -5 1 -9 "1 -7 -5 -8 -9 -5 -4 -8 -61-18-15
-5 -5 -6 0 -7 -2 -7 -5 -11 -9 -7 -5 -8 -81-16 -15
- - 1
BCP 9810-B-4-1 CS BCP 9810-B-4-2 Cs
-1 -- 1 -7 0 -2 0 -2 2 -
-5 -3 -2 0 -1 1 3 o 2-15 -7 03 0 2
-4 -4 -3 1 3 -I -] -l -13 -15 -7 -1 -2 -2 -5 0
-4 -4 -3 1 -2 1 2 2 -15 -14 -8 -2 -3 -3 -7 -1-5 -5 -6 L0 -4 - 1 0 -12 -13 -9 -7 -8 -5 1-12 -5
-8 -6 -5 -1 -5 -2 0 -1 -Hl -11 -8 -11 -9 -13 -9
18.513"
2 5/1611TYP
, 3 15/32" TYP0.5" o LEVEL
r=
8.0"
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C) CD -- 10 c - ('4z'- co -z (3 -o 0 C ) D Q
-N P- N4 ('4-7 0 C (31 \Dc)
L.7 CD '.0 -- C'4 - CO F-, CM t. CO, LP (N4 ('4C'4 (' C4 10 co) (' 01 C) M CO - :I r ('4 -7r
r - - (' C-4(' -7 ' 'D r, f- .0
LI ~ l C) -7 3 -C -Z3 W.. r-5 ( C '-7 C:;CL (' C14C 0- C - C S) CO 00 P- -7 r - C*
C* C')
C/7
Q) U
) ('4 1 0
ct LI) 0 C) -C) C) ) C)( C) 0) ') U ) C 0 C) CD C-) ) C
CL0 --7' -T '0 U) 0o1- ('a) oiC4 r'4 (
C'0C
CL CL(D C3CCCD C
m - ) C ) C), 0 ) I ) C) C - o) C \ E ) C C: ) CD (n CDCN 0_ ('C'1)(" "C K 4 cc '. ( rCO C C,
CD LI) _T - C) LA C C-4 L T C) r C ) C) -C) C) C)
CO LA - 0C) ('-so rCC CC N.4 r-
C) D -z'- CS) -- --C C r- O rl r Z c
Q ) CLA -7 C-4 C14 ('4j LAN ('4 -7 C) - -IZ
-C o CTN C) N -- "e\ C") m ) 0e j C , C 'o-7 so r-()
CD
-3(C C) \ U-\ LA 0, L C) so C) rl, AD U"lco) -7- uL D '-
U ' ", N N' . ) C" , C m' a') c' r (-,4 mO -Z o)4') -z ('4 ('4 M" CI) --T (n (('o ('r--- 0C
LU
C14 U')I U -
-7
)I0 0. 0)C) C C) CD Lr\In U'L L ) L A A C, LA UN LAU A C L
I 00 -P C14 C' Z LI) so C- o N 3* 10C C ' C'-7 L\- C
co M A U'\ C\ LA U LA C) LA C LA' ) LA\ C) U", C) LA Cz) U') C) LA.- m ('4 U-) T-- C) C) LA N C LA r-- 4C) C4 LAr f- C) (' LA\ N.
xC 0 C'4 C-4 ('4t (4 C")j C", M" r-\ -.r7 -- t -
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Co (NJ M) JD -:I" C) m ~ C) f\ (NCO ~ ~ ~ ~~C Co Co -o Co 0'c o00 0 0 00 C)\ -\ owo ~ cc Co 00 co-
0 M C,- C1 D - m \ 0 CO r_- - CD u, -T - -
z 'D0 w CD C-, -T C) (N -~ CN4 Id LA\ '.0 '. -7 CO CO (Dw~ (N r o ) Coo C- -\ Co \ 0) Co Co Co Co' Co Co Co C CD C)
CImo U'\ a) '0 M) Co Co - C:) UN (- CN (. 10 r Co0
m~ OD' MoCo C ) CD m' -:! Cj (N x Ln U-\ '. 'D0 C(N oN C) ffNr - r- 00 Co) Co CX-) Co Co Co o r- Co Co Co C C 00 ' a, o', -
L C o m- U-\ Co '0 ) - (N o - A U'\ cc :I - in LD C-\-o - - WN '00 Co m4 o- 0N 0N _ C 4 C ( N ' N Mf M( _: - :r
- ~ ~~~~~ -i r N o C o C o C ) C - - -N -N -N -( (- -~ -a
rox (N- 0o -T r- C' (N C N4 _. o ) - (J C) 0o Co-\ cn
-< - ) Co NJ 0 cc, 'D0 Co C(N L C) -T C 0 -\ L\ U (\ - - 'D0 - N
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- LL ' ) c
(NJ~ ~~~ CD o. C) o. Co o( oN- - 0. ) ' N N N ( C N 0
Co ~ - c0 0 C( - N -7 UI r- w. m. (NT (N- Co Co Co) Co Cm) - -
Lin L).
Ln
Co Co o o (
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C
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C) II (N - (N ( 0 Q) 00- ~ C o o - N (
-7 LA r, ( - 0 ( O'% 10 O'\ (n (N L"\ -o '0 a,\ Co\ CCA-N -Z (N C0 a, LA 10 '0 '0 0 0 ' '0 '0 0
-T~( (N (1CN (cN (N (N (N (N4
C) -7 '0 CC rN- (NJ CX -T LA 0') - '0 (- LA' C) C -r 0 Co' C'r,) CA N o (N\ LA\ r- C) M LAN 0\ - LA' C) LAl r- Co ) C(N -:r
- 1 (N 4 (N 4 (N 1 (N CA -.7 -Zr -11 -Z L ULA uLA
CO
(DC -zr (N , Co o '0 '0 mA r- - N 4( C 14 M 00C C) C)m4( A( LA C)-T co fA( - -T m -T Co C - CA '0 r-,
(Ai - ( N N CA -r -3- -Z LA\ LA\ '0 '0 '0 '0 '0
X( c) - r LA (cr\ LA\ C) C) 'aoCo C)oC C C LA Co) Co- mA ( N ' - L o C N ( -:T Co mA ( Co Co ' ( --r- 1 - l mN ( N A C -7 -:1 -zr LA LA LA LA'0 a C '0
LU
C14X
Q) C A Co LA (N Co LA' CA Co\ Co LA Cr A 0 U'\ Co - C 0 C N
- 00 - C'. (N T'- - - L ' (N co (71 0o C C) C) C)
Co. LU t--u
LA\ LA C) LA C aC LA C) LA C) LA CD LA C) C C- C(N LA (N C) ( LA (N C) (N4 LA r- C) (N4 LA '0Z ( CoC 1
- 4 (N (N (N N Cn A C A C A
C) 00 (N4 '0 rN-~ _ 0 ' C - Co'rN A - C LA' LAa) ( A ( ) C C14 - (N \ r C - C)' C) -7r -:T LAr Cor ( C
=1 - (N*' (N (N (N -zt O M Cr - C) U\ (
z C)T -o C A C - - -o (N LA M CA r '0 ' fo CoI LA- CA
CD ~ ~ '0 '0 Cor Ll -r '0 Co CA w ' \D m \.o LA C)4 - co C)cll Cr\Lr\- -- - -M -- ( "\ Nr (N C*- TA CA -~ CA "I
C- )C o L N L Co - C - C, : Co '0 Col '0 Cr (N1 U-\ \ CO Co\
Co CA0 co 10 -T -' CA C)r CD (N - L.(0A C L )
(UN (N L - N C o Co o Nr Co r CA uN \ '0 '0\ (N C mU o - (N N ( 10 -rl -o LA LA '0 '0 (N (N Co Co Co
LA
wU ) ) C) '0 C) 0 ' 0 C) C) (N\ 0 N '0 LA N LA C) CA \
o c- -- Nr CA-Z - D r, LA 0A0 '0 '0 N (N Co CO
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0) Co)j LA A ) C) C) C) C) C) LA\ C ) LA 0 UN C) L % C) C C) LA C- ( C*- A Co '0 LAZr - (N\ Co (N LA r- Co '0 C o'r 0 Co C- C-
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IMPERFECTION MEASUREMENTS
(x lo-3 in)
BCP 9121-A-5-I ES BCP 9921-A-5-2 ES
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IMPERFECTION MEASURFMENTS
(x io3 in)
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IMPERFECTION MEASUREMENTS
(x 1o-3 in)
BCP 9921-A-8-1 DS BCP 9921-A-8-2 DS
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2''- 6
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EXPERIMENTAL AND NUMNERICAL ANALYSIS OF AXIALLY COMPRESSED CXRCU--ETC(U)OCT 81 N R BAULD F33615-79-C-3030
UNCLASSIFIED AFWAL-TR-61-3156 NL22 AIflffffllllffff2EEE~hhE
7m EA1275 DATNU hV O E S EARChINh E E I 11
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11120
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L.. LAl (N M (N -:r r- "N m Mw) w ON a% m C 000
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IMPERFECTION MEASUREMENTS
(x 1O-3 in)
BCP 9817-B-7-1 BS BCP 9817-B-7-2 BS
1 _9_ 6 1 0 1 -3 L.-7 -5 1 1-2 0 1 0 2
13 10 1 -5 1-8 5 I1 -3 -4 -3 -3 -'18 12 3 -3-I - 1 6 1 -1 -2 1 3
23 17 7 2: 0 3 13 10 5 4
23 17 10 5i4 7 16 9 7 5 6 10
21 15 8 7 5 7 i 20 12 10 10 8; 12 _
15 12 9 9 8 9 21 13 15j15'13 15
BCP 9921-A-7-1 BS BCP 9921-A-7-2 BS
S40'3 _5_ -1 -5 0 9 8 3
12 1 -2 15 19 6 -2 5 25 31 17
15 3 12 19 12 _ 15 35 45 31
21 9 4 5 13 21 18 11 22 38 41 32
22: 12 5 4 10 18 23 17 26 361 37 32
21 13 7 7 12 17 27 20 25 32 36 38
18 13 11 11 12 17 31 32 33 39,
I " TYPLEvEL
_L U1 ,2,,,12" TYPI P
TYP3r2'' -
16.0" -
- -7
92
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APPENDIX B
STRAIN, END-SHORTENING, AND IMPERFECTION MEASUREMENTS FORTEST PANELS WITH UNSUPPORTED STRAIGHT EDGES
AND CLAMPED CURVED EDGES
TESTING PROGRAM B
93
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IMPERFECTION MEASUREMENTS
(x i0-3 in)
BCP 9824-A-2-I CF BCP 9824-A-2-2 CF
-4 -6 +1 +7 0 -14 -l 1-8 -2 +3 II -12 -6 0 +6 i+18 +13+3 1 1 1 -6 0 3
-8 0 13-5l12 I-7 +2 +3 -8G12 -8 0 -5 +5 +16 418
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-9-1 -12 -9 -II -1913 -8 +3 +4 -6 10 -5 -7 0 +9 +16
-10 -13 -13 -12 -13 -15 -13 -1 +9 +3 -4 -9 -8 -3 - +4 +12 +20
BCP 9810-B-4-1 CF BCP 9810-B-4-2 CF
+201+12 +4 0 1 0 -1 +2 +3 +8 1 +1 +1 +8 +5 o -0 '-2 1 '-28 -15+22 +14 +5 +1 +2 +2 +6 +9 +16 -+1 0 +6 +4 -3 -14 -18 -23 -
+21 +12 +4 +1 +1 0 +7 +9 1+19 0 -2 0 0 -6 -13 -I'-19 -24+33 +25 16 +9 +8 +6 +9 +11 +18 0 -4 -1 -5 -10-14 -14 -16 -6
+33 26 17 +12 1+10 +8 i+1 1+14 !+20 -7 -10 -10 -11 -6 -6 +6-I- !i -' .
17. 513''
2 3/16''P
3 9/16" TYP0.5" LEVEL
II
2F T
8.0"-8 - 5 _
This imperfection data is questionable. Imperfection measuring device
was not mounted accurately enough.
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IMPERFECTION MEASUREMENTS
(x io-3 in)
BCP 9921-A-6-1 EF 3CP 9921-A-6-2 EF
1+28J+35 +36 +23 O -5 +28 +50+52 ,+0 13 26 +14 0 +2 !+24 :+44 +69+241+35 +38 +30 +Ri +8+35 , +52+56 +731+48+33 + 02 +35 +59
+261+33 +42 +33 ! +18 J+4 _ 1+55V 6 , +52 ,42 +40 +30 +22 +26 +1,? +62 +72+++ i--1---+32 1+36 1+44 +38 +26 +26 i+50 '+ +61 30 42 +43 +38 +32 34 +52 '+62 80
+39 +36 +45 +40 +37 1+40 +39 +64 +72 +48 +46 +48 +43 +44 +45 +6l +69 +85
_+64 +72_ +48_ +4 +8 4 4
BCP 9817-B-5-1 EF BCP 9817-8-5-2 EF
+68+551+31 o+Io l40 +59 +66 +25 +24 i+2j' ,. 0 +1 +2 2 !+525 1+ 3 +2 0 1++66 +54 +;20 +12 j+1+44 +s 8 +5 1+ +8 +~2~+65 +57 '+48 '+36 +28 + 30 +51 '2 5 + + 32 29 +21+32 +33 +34 +28 1+5 1+13 +3
0 +29 +21
+60 +61 +56 +41 +40 +44 +53 +57 4Ao + +3 +2 + +
+55 +53 +55 +48 +50+5i,5+58+56 + + + +
S+2 29 32 1+30 i+ 25 +25 +32 +33
17.513''211, TYP
3 TYP
LEVEL"IT -.1 • il II-- I
1 -- 2
2''TYP 312.0 T'-
- S
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IMPERFECTION MEASUREMENTS
(x o-3 in)
BCP 9824-A-4-I AF BCP 9824-A-4-2 AF
+31 +221+15 +5 O -2 +51+10 +1] +.)8 +16 10 0 0 -5 +2 1 +6 +7
+32 +25 +16 -4 -21 +l1 +8 I+13 +20 +28 +19 +12 +2 +I "4 +4 !+ 10 +6
+34 +26 +19 +6 +4 +41+11 +17 +22 j+16 1 1+16 +" -2 0 +;i !+13 +6
+39 +31 +22 +10 +8 +io +19 +25 +29 +30 +30 i+27 +16 +l 1i+15 +31 +23 1+11
+45 +35 +27 +16 +14 +17 +26 +30 +37 +34 +31 .+32 +22 +17 +2 +39 '+34 '- 9
+451+37 +29 +21 +22 +24 +33 +40 +46 +32 4+33 +34+23 +19 +25 +4 1 +36 +16
+43 +37 +34 +28 +31 +33 +43 +50 +62 +34 +36 +35 !+28 +29 +32 +47 42 +3CF
BCP 9817-B-8-1 AF BCP 9817-B-8-2 AF
+30 +14 +6 0 o-1 +5:+15 +30 +15 11+139+92 +3 0 38 -6 6 -961-33
+29 +16 +9 +3 +5 +2 +7 +22 +38 +179+132+88 +45 +3 -25 -50 -72 106
+38 +25 k16 +10 +10 +10 +15 +28 +40 + 1674+127+88 +53 1+21 -9 -30 -42 -55
+47 +33 k25 -19 +18 -19 +24 +34 +-41 +158+124+90 +59 +33 +11 -5 -11 -I1
.+60 +43 I-36 t+29 +28 1-30 34 +39 +46 +145+117+90 +(65 -+46 +28 +16 +16 +21
69 50 44 +38 +36 38 +41 +45 +48 +130+1111+90 +72 4+6 +46 +39 +443 !+52
71 8 51 44 +42 45 +50 +50 57 +_114+10390 +75+67 +61 +60 !+67 +75
17.513"
2 3/16'TYP
i- 3 9/16" TYP
1'' I LEVEL
2"TYP 4_ 5
6
I 7I _- 8I I - 9
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IMPERFECT0N MEASUREMETS
x 10-3 in)
BCP 9817-B-6-1 DF BCP 9824-A-1-2 DF
+19 k12 +6 1+3 0 0 0 0 -0 -10 -12 -16 -11 1 11 -3 -3 0
+12 +6 -2 -7 -9 -6 -6 -3 -9 -15 -16 -20 ,-13 -9 -12 -12 -1 +7+10 +4 -5 1JO -12 -9 -6 +2 +3 -14 -15 -16 -12 -11 -9 -8 O+13
+ 12 + 6 -I -6 -II -6 -2 - +12 + 2 1 -9 - 10 - 1 1 -8 -7 -6 - + 7 + 17+ + 7 1 0 -3 - 7 -5 + 3 + 18 + 3 1 + 1 + 1 - 3 -2 0 + 3 + 4 i+ I4 + 29
+5+2 -3 -4 -9 -5 +3 +19 +31 1+-11 +5 -1 +21 +4 1+3 + r 1+17+30'
5
17+2+ 1, I : =
14 +9 +6 1+4 0 +2 +7 +16 +23 +17+12 +6 +11 +15 '+20 +28 +38
BCP 9824-A-1-I DF BCP 9817-B-6-2 OF
+71 0i +2 +5 0 - 2 +6 18 +19 +13 +10 +8 0 +2 +4 +i0 +15
+6 +3 +1 +3 +3 + +3 -4 +5 18 +16 +12 +8 +5 -4 -5 -1 +11 +22
+8 +5 +6 +7 +6 +2 +1 +8 +20 +15 +10 +6 +3 -7 -9 -5 +9 +24
+13 + I1 +10 +12 +9 +6 +8 15 +23 +18 +14 +9 +4 -5 -7 -21+12 +26
+19 +18 +14 +16 +16 '+15 +14 +22 +29 +17 +14 +9 +5 -4 -6 -I +13 +22
+24 +20 +18 20 +20 '+19 +21 28 +36 +14 .+1l +7 +2 -4 -8 +1 +10 +17
+30 +27 '2 5 k25 +29 +28 +32 +40 +50 +8 +8 +7 +5 +2 +7 +10 +1R +25
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I9/161"TYP
2 11/32" TYP1'' 1LEVEL
T- 2
2 " T Y 1 4
16.o0" T 67
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I.MPERFECTION MEASUREMENTS
(x ]o-3 in)
BCP 9921-A-7-1 BF BCP 9921-A-7-2 BF
+30i+27 +22 p14. 0 -7 -8 -3 1-6 +9 10 1+9 +5 0 -3 -6 1-8-10
+61 +45 +28 k15 -1 12 -12 +-4 -14 +21 +20 k15 +10 0 -10 -20 -29 -36
+8L +60 +36 11 13 +34 +25 k17 -4 1-1 6 -26 i-40 -57
+24 +2160 +10 + 4 - +. 4 03 - + -2 5~-- - -1 -6 ,+83 +60 +35 +14 -1 -8 -]1 -10 -10 +39 +30 +21 +11 -2 -14 -26 -48 -71
+63 +51 +31 +13 +2 -5 -5 -8 - +3 +33 ,+24 +12 -3 -161-26 _-43 -64- - I -25
+44 +36 +24 +12 +3 -2 -1 -2 -2 +33 +30 +22 +12 -2 1-12 -17 -38
+24 +21 ]+16 +10 +4 +3 + 0 +2 +21 i+19 +13 +7 -3 -3 -8 -11 -15
BCP 9817-B-7-1 BF BCP 9817-B-7-2 BF
+6 1+ +3 +2 0 -2 3 - - 1 +1+4
+12 +8 +3 +2 - 1 -5 -8 10-1 6 1-.16 +12 1+5 -2 -6 -5 0 +5 J+2+13 +8 +3 0 -4 -8 -9 -12 -16 +20 +13 +8 0 -3 -4 0 +4 +1
+18 +12 +5 +1 -2 -6 -6 -7 -9 +23;+16 +6 +1l-3 -4 -1 +2
+13 + II +5 +1 -2 -5 -5 -5 -6 +20 +15 +7 +2 -3 -3 -3 -2 -9
+16 +5 j +2 0 -2 -4 -3 -3 -4 +19 +14 +10 +5 ' 0 -1 -2 -2 1-13
+4 +4 +3 +3 +2 0 +1 0 0 +14 +12 ,+10 +8 i +4 +3 +2 0 -9
8. 156"
1 1 /64'TY P
1 33/64" TYP
"£ I LEVEL
j A1 10 IIi _-2
2"TYP 4
6 OI ___
_6
7I __8
9
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APPENDIX C
STRAIN, END-SHORTENING, AND IMPERFECTION MEASUREMENTSFOR TEST PANELS FOR TESTING PROGRAM B
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is. 5CQi
.I
I II I
3 4.i 7 F I ~~
. - - 3
1 6 4L
FIGURE Locations for strain and imperfection measurements for 16- x I?panels with [0/9012s fiber pattern and unsupport-d straiohtedcnes. For 16 x 12 panels with [0/+45/90]s fiber pattern and
j simply-supported straight edges only the axial strains at thethree interior locations were recorded, and the imperfect datawere recorded for the seven interior imperfection grid lines.
a (Circumferential dimensions shown correspond to the panelswith unsupported straight edges. Subtract one inch for simply-supported panels.)
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Imperfection measurements (xlO'3 in) for l6x12 panels with fiber pattern[O/+45/90] s and simply-supported straight edges (curved edges clamped).
Collapse load in parentheses.rounded edges
DS-A9-l (4600 lb) freely DS-A9-2 (4975 Ib) 30 in-lb on side bars
31 8 8 6 8 6 2 6 3 3 2 8 6 3
-2 7 7 3 4 7 0 5 4 4 3 5 8 7
-2 7 7 3 4 5 -1 8 4 3 3 4 9 6-2 4 4 3 1 3 -3 8 2 3 2 3 7 6
-4 2 2 -1 -2 1 -2 4 -2 -2 -l -l 6 3
0 2 1 -1 -2 I -2 5 -1 2 2 1
1 1 0 -l -2 -1 0 1 1 3 4 3 6 3
DS-A1O-I (5775 Ib) 10 in-lb DS-A1O-2 (5510 ib) 30 in-lb on side bars
0 4 5 4 7 7 6 19 13 6 5 8 12 9
-4 2 4 4 6 6 9 33 22 5 2 7 12 10
-7 0 7 7 6 7 9 33 28 2 -2 4 15 18
-10 -2 3 4 4 4 7 30 31 1 -4 2 18 22
-12 -5 2 0 0 3 3 30 24 01-10 -3 16 17
-12 -4 1 1 1 1 0 0 21 -1 -7 -4 10 13
-6 -2 0 -I 2 0 -l 19 1 i-2 -4 -I 6 8
DA-AII-1 (5160 Ib) nearly freely
-61 -7 -3 0 0 -6 -2
-10 -6 0 5 -1 -8 -8
-7 -4 7 10 4 -6 -7
-6 -7 6 10 3 -8 -12
-40.-- -I 5 I -9 -13-6 -7 2 4 0 -7 -8
-6 -4 -2 0 o -4 1 -7
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Imperfection measurements (xlO-3 in) for 16-12 panels with fiber pattern
[0/901, and unsupported straight edges (curved edges clamped). Collapseload in parentheses.
DS-BII-I (2460 lb) DS-Bll-2 (2715 lb)
8 8 3 8 9 11 10 11 16 9 6 5' 8 6 7 7 8 13
I 1 1012 9 9 9 4 3 6 8 9 7 6 10 1391 61 6 61 8 8 6 6 5 -2 2 7' 7 9 8 6 10O 12
51~ l0 2 4 3 4-8 -2 4 i 7 .7 I 6 5 81 HI
0 2 1 2 3 4 1 6 1 0 -1 2 -7 3 6 5 3 .. 2 5 9-7 -2 -l -2 -2 - 1 -3 l 1 6 1 -10-:O 2 1 1 - 1 5 9
-7 -3 - -3 -3 -3 -3 70 3 1 6
DS-BIO-I (2300 ib) DS-BO-2 (2495 lb)
8 3 1 0 4 8 13 12 13 16 12 7 5 7 7 9 13 21 33
11 5 1 3 9 14 12 9 11 23 14 10 12 11 13 17 38 33
13 6 4 6 10 18 14 9 8 16 9 5 6 6 8 13 21 31
5 -I -1 0 5 11 8 2. 0 If 7 5 6 4 8 11 16 23
4 0 -1 0 4 10 7 0 -2 8 1 3 2 1 4 5 7 10
4 0 -2 -1 3 7 6 0 -4 3 2 1 2 2 4 4 3 5
4 2-I _ 1 6 4 1-1 2 2 1 2 2 3 2 1 4
DS-B9-I (2165 Ib) DS-B9-2 (2410 Tb)
-6 -2 3 5 5 10 13 14 23 -4 -2 -2 2 4 8 i0 16 23
1 3 6 8 7 13 15 11 11 -1 -1 2 4 7 10 10 16 29
5 3 3 8 10 14 16 1O 8 -1 0 2 3 7 12 11 14 23
7 2 1 6 5 9 12 6 2 -1 -2 2 2 5 9 8 12 18
8 2 -1 3 2 6 6 0 -1 2 1 1 2 3 8 8 10 14
13 4 1 5 6 6 7 4 3 4 3 3 3 3 9 7 12
8 3 1 3 3 3 6 3 3 3 1 1 1 1 3 44
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APPENDIX D
USER'S MANUAL FOR COMPUTER PROGRAM~ CLAPP
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. TCLAPP USERS MANUAL
1. TITLE CARD (18A4)
Columns 1-72 Problem description
2. CONTROL CARD (815)
Columns 1-5 IRUN - Takes integer values 1, 2, 3,according as the completion of an
analysis requires 1, 2, 3,submissions of the program.IRUN = 1 for the first submission,IRUN = 2 for the second submission,
and so forth. Valid for nonlinearanalysis only (IBIF = 0). IRUN
#ifor any analysis that is a con-tinuation of a previous application
of CLAPP.
6-l0 IEX = 0 perfect panel or plate
imperfect panel or plate
]1-)5 IBIF = fO nonlinear analysis
1I linear bifurcation analysis
0 flat plate analysis16-20 NFLAT = f
curved panel analysis
0 x and y coordinates must bepunched for input. Variablegrid capabilities.
21-25 NAUTO=11 Automatic generation of x and
y coordinates with uniform, butpossibly different, spacingsfor the x and y directions.
0 Initial imperfections are repre-
sented by a mathematicalexpression.
26-30 LGRNG =I Initial imperfections are repre-
sented by a two-dimensional
Lagrange interpolatinq function.
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f0 When the load-deflection curveis generated in seqments thetape NTAPE contains the infor-mation required by the programto continue the calculations
beginning with the last load-level for which a convergedsolution was obtained. To con-
tinue calculations set INDEX =2, 3, ... and NUSTRT - 0.
31-35 NUSTRTI It may happen that it is desir-able to adjust the loadinqsequence to begin calculationsfor a second segment of the load-deflection curve. To do this setINDEX = 2, 3, ... , NUSTRT = I andreset the input data for PZSTRT,PXSTRT, PYSTRT, AND ZINCR, XINCR,YINCR.
36-4o NCURVE =0
3. CONVERGENCE CRITERION CARD (FIO.0, 215)
Columns 1-10 EPSI - Convergence criterion that determinesiacceptable displacements at a given
load-level (order of 10-").
11-15 ITMAX - Program terminates if converqence atany load-level has not occurred
within ITMAX iterations.
16-20 LEMAX - Program terminates after processinqLEMAX load-levels as collapse orbifurcation has not occurred.Resubmit program with IRUN = 2.
4. GRID PARAMETERS CARD (815)
I Finite-difference grid pointsnumbered consecutively along across-sectional circle
Columns 1-5 NSCHM =0 Finite-difference grid points
numbered consecutively along agenerator
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O Panel has no cutout6-10 ICTOUT
I Panel has a cutout
11-15 NCOLS - Number of columns of grid points.
16-20 NROWS - Number of rows of grid points.
21-25 IROWI - Number of the row in which theside of the cutout nearest thefirst row of grid points lies.
26-30 IROW2 - Number of the row in which theside of the cutout furtherestfrom the first row of grid pointslies.
31-35 ICOLI - Number of the column in which the
side of the cutout nearest thefirst column of grid points lies.
36-40 ICOL2 - Number of the column in which the
side of the cutout furtherestfrom the first column of grid
points lies.
___________ NCOLS
ICOLI ICOL21_ 2 3 4 0 11 12
- ~ I If I
IROW IFOR NUMBERING OF NODESALONG A GENERATOR
NROWS CUTOUT NSCHMOI
IROW 2
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NROWS
IROWI IROW2
I I FOR NUMBERING OF NODES
2 1 ALONG A CROSS SECTIONALI CIRCLE NSCHM=I
3ICOLI L -
NCOLS CUTOUT
ICOL2 -
11
NOTE: Node numbering must originate at the upper left-hand corner of the
finite-difference grid.
5. PANEL DIMENSIONS CARD (3FIO.O)
Columns 1-10 XDIM - Lenqth of a panel parallel toa generator.
11-20 YDIM - Length of a panel along a crosssectional circle (not the pro-jection).
21-30 R - Panel radius of curvature. (Anynumber will suffice for a plate.
6. BOUNDARY CONDITION IDENTIFIER CARD (815)
Columns 1-5 NCASE1 1
6-10 NCASE2( 2
11-15 NCASE3
16-20 NCASE4 = .3
21-25 NCASE5
26-30 NCASE6 -
31-35 NCASE7
36-40 NCASE8 5
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NCASE_ identifies a boundary of the panel as indicated in the accompanyingfigure. An integer from I to 5 is assigned to each NCASE accordinq as thedesired support condition along the edge identified by NCASE is one of thoseshown above.
NCASEI
z Direction of az M
z NCASE7 M A Generator
NCASE3
7. RIGID BODY CONDITION CARD (415)
Columns 1-5 IRBI 1 Tangential displacement parallelto the boundary identified by
6-10 IRB2 IRB is precluded at the mid-point of the boundary for an
11-15 IRB3 even number of grid points, orat the grid point nearest mid-
16-20 IRB4 point for an odd number of qridpoints.
0 No modifications to boundaryIRBI=I U=O L conditions are made.
IRB3=l, U=O 1
8. INITIAL-LOAD CARD (4F15.O,15)
Columns 1-15 PZSTRT - Initial-load normal to the panelsurface. (Positive away from thecenter of curvature.)
16-30 PXSTRT - Initial-load parallel to a genera-
tor of the panel. (Positive inthe direction of increasing gridpoint numbers.)
31-45 PYSTRT - Initial-load tangent to a cross-sectional circle. (Positive in
the direction of increasing qridpoint numbers.
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46-6o XDISPO - Prescribed initial axial end-displacement. Negative for com-pression.
[0 Prescribed loads61-65 MDISP
I Prescribed end-displacements
23 4 1 12 2334
12 2
23 334 PXSTRT 4
PXSTRT
POSITIVE DIRECTIONS FOR PXSTRT POSITIVE DIRECTIONS FOR PXSTRTAND PYSTRT FOR NSCHM=O AND PYSTRT FOR NSCHM=I.
9. LOAD IDENTIFICATION CARD (415)
1 Concentrated load at grid
point number LNODE.
2 Line-load along row number LROWof the finite-difference grid.
Columns 1-5 LCASE3 Line-load along column number
LCOL of the finite-differencegrid.
4 Uniform distributed load overthe entire surface.
6-10 LNODE - Number of the finite-differencegrid-point at which a concentratedload is applied.
11-15 LROW - Number of the row of finite-difference grid points along whicha line-load is applied.
16-20 LCOL - Number of the column of finite-difference grid points along whicha line-load is applied.
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10. LOAD INCREMENT CARD (3FIO.O)
Columns 1-10 ZINCR - Load increment normal to the panelsurface.
11-20 XINCR - Load increment parallel to agenerator of the panel.
21-30 YINCR - Load increment tangent to a cross-
sectional circle of the panel.
Positive directions for load-increments are the same as those for the initialloads.
If IEX # 1 cards 11, 12, and 13 are not required.
11. INITIAL IMPERFECTION CARD (5FI0.0,15) Required only if LGRNG = 0 and IEX =I
Columns 1-10 WO - Amplitude of initial geometricimperfection.
11-20 CONSi - Wave number of the imperfection
associated with the direction ofa generator of a panel (n/halflength of panel)
O Clamped curved edges and unsup-
ported straiqht edges.21-30 CONS2 =
b Clamped curved edges and simply-
supported straight edges. b isone half of the circumferentiallength of a panel
31-40 XO - x-coordinate of geometric center
of panel measured from lower lefthand corner
41-50 YO - y-coordinator of geometric center
of the panel measured from thelower left hand corner
Initial imperfection has the formWO(x,y) - Wl*(l+cos 7r/a)(l-(r/b) 2 )(Clamped at curved edges - simply-supported along the straight edges)
51-60 IMPFORM =
Initial imperfection has the formWO(x) = WI*(I+cos 'n/a)(Clamped along the curved edgesfree at the straight edoes)
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12. IMPERFECTION-GRID PARAMETER CARD (215) Required only if LGRNG = 1 and IEX 1
Columns 1-5 MX = Number of grid points alonq agenerator for which discrete valuesof initial imperfection are known.
Spacing of these points is requiredto be uniform.
6-10 MY = Number of grid points along a crosssectional circle for which discretevalues of initial imperfection areknown. Spacing of these points isrequired to be uniform.
MX or MY can not exceed 10 for the present dimensions of the program.
13. IMPERFECTION DATA CARD (1OF8.0) Required only if LGRNG = 1 and IEX = 1
A single card contains the known discrete value of initial imperfectionfor every grid point in a row of the imperfection-grid. Thus, MY cardsare required: one for each row of the imperfection-grid. A row isconsidered to be parallel to a generator of the panel. Imperfectionvalues are positive away from the center of curvature of the panel.
Imperfection-grid size cannot exceed 10 grid points in either directionunless internal dimensions are modified.
Imperfection-grid is parallel to finite-difference grid with origin assholen in the figure.
Direction of a
Third Card, Etc. * Generator
Second Card Row 2 . . . .
First Card Row 1 = - - 0 _
14. NODAL COORDINATE CARD (2FIO.O) Required only if NAUTO = 0
Columns 1-10 x-coordinate of a finite-difference gridpoint
11-20 y-coordinate of a finite-difference gridpoint
These cards are required only when NAUTO = 0; i.e., whenever a variablefinite-difference grid is required.
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15. STIFFENER CARD (415)Fo no stiffeners
Columns 1-5 NSTFR I stiffeners included
6-10 NSTYP throuh 8 - cross section type(see below)
L
11-15 NSLOC = 0 located on outside of panel (+)I located on inside of panel
16-20 ISSPC =o spaced on all qrid linest1 variable spacing
16. STIFFENER CROSS SECTION INPUT CARDS only if NSTFR = I
The number and required input of these cards depend on the choice of
stiffener cross section type (NSTYP) above.
NSTYP = I (2FIO.O) (2F1O.O) rectangular plate
(1) Columns 1-10 HGHT = h11-20 WDTH = b
(2) Columns 1-10 SEMOD = elastic modulus11-20 SGMOD = shear modulus
NSTYP = 2 (4F1O.O) (2Fl0.O) symmetric I beam
(1) Columns 1-10 HGHT = h (total - tf) t I11-20 WDTI= b21-30 FLTHK = tf L
31-40 WTHK = tw
(2) Columns 1-10 SEMOD = elastic modulusi1-20 SGMOD = shear modulus
NSTYP = 3 (5F1O.O) (2FIO.O) non-symmetric I beam
(1) Columns 1-10 HGHT = h (total - tf)11-20 TWDTH = bi2 1-30 BWDTH = b231-40 FLTHK = tf r
41-50 WTHK = tw
(2) Columns 1-10 SEMOD = elastic modulus11-20 SGMOD = shear modulus
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NSTYP = 4 ('Ff10.0) (2F10.0) inverted T f w
(1) Columns 1-10 HGHT = h (total - tf12)11-20 WDTH = bf
21-30 FLTHK -tf
31-40 WTHK =tw
(2) Columns 1-10 SEMOD =elastic modulus .
11-20 SGMOD shear modulus
NSTYP =5 (4F10.0) (2F10.0) T -beam- -
(1) Columns 1-10 HGHT = h (total - t f/2)11-20 WDTH = b21-30 FLTHK = tf31-40 WTHK = t
(2) Columns 1-10 SEMOD - elastic modulus '~11-20 SGMOD - shear modulus
NSTYP =6 (4Fl0.0) (21 10.0) C beam
(1) Columns 1-10 HGHT =h (total -tf i11-20 WDTH =b
2 1-30 FLTHK = tf L
31-40 WTHK = t .4
(2) Columns 1-10 SEMOD = elastic modulus
11-20 SGMOD = shear modulus
NSTYP = 7 (4F10.0) (21 10.0) L beam
(1) Columns 1-10 HGHT = h (total - tf/12) r11-20 14DTH = b21-30 FLTHK = tf31-40 WTHK = tw 4
(2) Columns 1-10 SEMOD = elastic modulus11-20 SGMOD = shear modulus
NSTYP = 8 (4F10.o) (5F10.0) (2F]0.0) user's choice 4
(1) Columns 1-10 SAREA = cross section area11-20 CEI = 1st principal moment of inertia, Ivv21-30 ETAI = 2nd principal moment of inertia, LM?31-40 ALPHA = angle from hori7ontal to §g-direction.
in radians
(2) Columns 1-1 CED = distance to contact point, g-direct ion11-20 ETAD = distance to contact point, I-direct ion21-30 CES = distance to shear center, 5-direct ion31-40 ETAS = distance to shear center, T-direct ion41-50 CONSTJ = twist inq constant, J
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(3) Columns 1-)0 SEMOD - elastic modulus11-20 SGMOD - shear modulus
Refer to figure on the next page for an example of these quantities
for the user's choice stiffener, type 8.
NSTYP = 9 (4FlO.O,15)(5FO.O) QUASI-ISOTROPIC HAT SECTION
(1) Columns 1 - 10 HGHT = h
11 -20 WDTH= b
21 - 30 FLNGW = b
31 - 40 STHK = t- - - - - - - - .
41 - 45 NLAYER = No. oflayers.
(2) Columns 1 - 10 Eli = elastic UNIFoRM scCr,*,V 7WrA'ClESS
modulus parallel to
the fibers of a lamina.
II - 20 E22 = elastic modulus
perpendicular to the
fibers of a lamina.
21 - 30 G12 = lamina shear modulus
31 - 40 PNUI2 = Poisson ratio associated
with stress along fiber direction.
41 - 50 PNU21 = Poisson ratio associated
with stress perpendicular to fiber
direction.
This stiffener cross section type accomodates fiber-reinforced
stiffeners where the fiber directions are alternately zero and 90
degrees. Midplane symmetry is assumed.
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Note that the stiffeners when located on the inside of the panel areinverted as depicted below.
.4
It __
5T/~ 0,1 aJ 7WIE 5riFFeAAEk OX.J 7-I
ouTrIp oF PANEL j.7jPE o PYAIFL.
17. NUMBER OF STIFFENERS (15) needed only if ISSPC = 1, NSTFR I
rolumns 1-5 NST = number of stiffeners if they are
not on each qrid line
18. VARIABLE SPACING STIFFENER CARDS (15) only if ISSPC = 1, NSTFR = I
Columns 1-5 NSROW = row number that locates stiffener(if NSCHM = 0)column number that locates stiffener(if NSCHM = 1)
One card is required for each stiffener, so there will be the samenumber of cards as NST above. The row (or column) numbers must be inincreasing order, i.e., 1,4,7,10, etc. not 1,7,4,10.
19. NUMBER OF LAYERS CARD (15)
Columns 1-5 KN - Number of layers in the laminate.
20. LAYER LOCATION CARDS (Flo.o)
Columns 1-10 Distance (inches) b(tween a layer surface
nearest the center of curvature and thelaminate reference surface. First layer
is considered to be the one nearest thecenter of curvature. Distances measured
toward the center of curvature are negative.
A card for the most remote surface of the last layer is required. Thus,there is required KN+I LAYER LOCATION CARDS.
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21. MATERIAL PROPERTIES CARDS (6FIO.O) One card is required for each layer.
Columns 1-10 Modulus of elasticity parallel to the
fibers of a given layer (lb/in 2 )
11-20 Modulus of elasticity perpendicular tothe fibers of a given layer (lb/in ? )
21-30 Poisson ratio associated with strainparallel to the fiber axis due to a stressperpendicular to the fiber axis
31-40 Poisson ratio associated with strain perpen-dicular to the fiber axis due to a stress
parallel to the fiber axis.
41-50 Shearing modulus of elasticity (lb/in 2 )
51-60 Angle between the fiber direction and a
generator of the panel. This angle ispositive whenever the fiber direction issituated in a clockwise orientation relative
to the positive x-direction.
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EXAMPLE THAT DEFINES INPUT QUANTITIES
FOR USERS CHOICE STIFFENER
C -- CEAI-T'CO/ID
CD COqrACT POINT
BETWEEN PFqAtEL
C &AND SrIFFLEAJER
_ _ x -
AREAA
.X .-t- "."r, ,.L
I - I T
"!r( ± cr'(r7
C -,TD = i.-"p + L
ETADD. Pn O-
Er, 5E
147
*U.S.Governmeflt Printing Office: 1982 5-009O5/4055
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