experimental and numerical methods for the prediction of wave loads in extreme sea conditions
TRANSCRIPT
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D. I. N A V.Dipartimento di Ingegneria NAVale
Academic Year 2010/2011
Experimental and Numerical Methods for the
Evaluation of Wave Loads on Offshore Platforms in
Extreme Sea Conditions.
Supervisor
Prof. Ing. Stefano Brizzolara
Co-supervisors
Prof. Ing. Claire De Marco - University of Malta
Prof. Ing. Tonio Sant - University of Malta
Candidate: Umberto Ghisaura
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Ad Angelina, Giancarlo, Stefano e Riccardo
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di GenovaII
Conservative form of the governing equations of fluid flow 52
Differential and integral forms of the general transport equations 52
THE FINITE VOLUME METHOD 55
Step 1: Grid generation 56
Step 2: Discretization 56Step 3: Solution of equations 58
MAIN FEATURES OF THE MESH 59
Physic models 59
Control Volume and Mesh refinement 60
WAVES REPRESENTATION 62
Free Surface Definition and VoF Theory 62
Progressive Waves 63
COMPARISON AND ANALYSIS OF DATA 65Comparison between simulations and tank tests 65
Spline Interpolation of the height. 75
Analysis of experimental non dimensionalized data. 77
Vertical Force 77
Horizontal Force 81
Pitch Moment 87
CONCLUSIONS AND FUTURE DEVELOPMENTS 91
LEGEND 93
REFERENCES 94
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di GenovaIII
TABLE OF FIGURES
Figure 1: Wave Theories Graph 25
Figure 2: Generated Wave Order 26
Figure 3: Wave Sampling - Wave Length vs. Period 27
Figure 4: Wave Sampling - Wave Height vs. Period 28
Figure 5: Wave Sampling - H/L vs. Period 29
Figure 6: Wave Sampling - Wave Height vs. Crank Length 30
Figure 10: KLC1 Calibration 39
Figure 11: KLC2 Calibration 40
Figure 12: KLC3 Calibration 40
Figure 13: Sawtooth test 41
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova1
ABSTRACT
Experimental and Numerical Analysis of the Wave
Loads on a Floating Wind Turbine Platform in
Extreme Sea Conditions
The aim of the research was to characterise the hydrodynamic surge, heave and pitch forces
of a floating wind turbine semi-submerged tension leg platform. A series of experimental
measurements on a 1/100th
scaled model were undertaken and the results were compared
with those obtained from a numerical RANSE model. Relevance and innovation consisted inusing a model strictly close to reality during experimental tests, and in using non-linear
waves both in the wave tank and with the state-of-the-art RANSE solver.
The geometry of the structure consisted of four cylindrical bodies joined to a central large
cylinder (5 meters diameter, 20 meters length) which supported the wind turbine tower by
means of eight tubular connections (3.3 meters diameter, 12.3 meters length). Each body was
composed of one cylinder (7.8 meters diameter, 20 meters length) with a further larger
cylindrical body (9 meters diameter, 7.8 height) to increase the stability.
The study concentrated on the prediction of non-linear hydrodynamic forces acting on the
complex structure. The scaled model was tested in a water wave maker in a fixed condition.Three separate load cells were used to measure the forces and moment components.
A preliminary study was dedicated to the verification of the second and third order Stokes
waves obtained with the wave maker by a sampling of the waves measured in the tank for
each of the reported test condition. The period of the water waves ranged between 6 seconds
and 1.15 seconds, while wave height varied between 3.37 to 10.7 meters.
The numerical RANSE model was based on a special non-structured (trimmed type) mesh
grid with anisotropic refinement in the three cardinal directions to ensure a good convergence
property with a limited expense in terms of total number of cells, while representing the
various geometrical details of the structure (such as the connections and the cylinders).
Experimental results were compared in a scientific and non-dimensionalized graphic form
with RANSE values versus the wave slope (k*H) and the Keulegan-Carpenter number (Kc).
Finally, a common engineering law for predicting these forces was identified.
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova2
INTRODUCTION
Survey of word offshore wind energy plants
Europe is the world leader in offshore wind power, with the first offshore wind farm being
installed in Denmark in 1991. In 2008, offshore wind power contributed 0.8 GW of the total
28 GW of wind power capacity constructed that year. By October 2009, 26 offshore wind
farms had been constructed in Europe with an average rated capacity of 76 MW, and as of2010 the United Kingdom has by far the largest capacity of offshore wind farms with 1.3
GW, more than the rest of the world combined at 1.1 GW. The UK is followed by Denmark
(854 MW), The Netherlands (249 MW), Belgium (195 MW), Sweden (164 MW), Germany
(92 MW), Ireland (25 MW), Finland (26 MW) and Norway with 2.3 MW. Based on current
orders, BTM, an independent consultancy company specializing in services pertaining to
renewable energy, expects 15 GW more between 2010 and 2014.
Main features of the current offshore plants
Current offshore installations are made by
high-power units, which allow to exploit
better the best offer from the offshore
wind resource.
The location at sea has the advantage of
better wind resources and therefore an
higher production of energy. Furthermore
it yields less turbulences into the wind and
consequently a better durability of
mechanical parts. It is not tooverlook the higher availability of
sites, since the on-shore ones are
subjected to saturation, even for
the difficult acceptance by the
involved people in the installation
areas.
On the other hand, there is a
complex set of static and dynamic
forces on the structure and on the
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova3
turbine which increase the difficulty of the challenge. Sea corrosion, higher wind resources,
ice on northern seas, far distances from the ashore which means using relevant electrical
equipment are the difficulties you find at the planning stage.
During the installation on site, there are procedures of transport, assembly and ready for use
settings much more difficult and different than onshore ones; thus times, expenses and
dimensions are in a different scale.
Studying floating structures, for the exploitation of wind energy, rise from the will of
reducing the environmental impact with the seabed and the needing to move the platform in
different places. The structure is done by two essential components: the floating platform
with its anchoring system and the wind turbine rigidly bound to the structure. Many kinds ofstructures have been studied:
-Semisub Dutch tri-floater
-Barge
-Spar-buoy with 2 tiers of guy-wire
-3-arm mono-hull
-Concrete TLP with gravity anchor
-Deep water spart
Recently a concept
wind farm made by a
unique huge floating
structure which brings
multiple wind turbines
has been developed;
this would improve the
stability of the whole
system and easier
accessibility for the
installation and the
maintenance.
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova4
DEFINITION OF THE PROBLEM
The idea which gives rise to the joint work of the two Universities is to evaluate the wave
loads of an offshore platform in extreme non-linear conditions. In this project the University
of Malta offered the wave tank and its competence in the construction of models, while the
Universita` degli Studi di Genova shared its proficiency in solving such kind of
hydrodynamic problems both in an experimental and numerical way.
The wave tank is made up of glass and its dimensions are L1* W1* H1=8m*0.75m*1m.The height of the water level from the seabed in calm water condition is D1=783 mm
Picture 1: Wave tank
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova5
The wave tank consists of the following components:
-one wave generator made by a swinging panel hinged on the bottom of the tank as shown in
Picture 2: Swinging Panel
Picture 2: Swinging Panel
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova6
-one frequency controlled electric motor which moves the panel by a crankshaft as shown in
Picture 3: Electric Motor
-two passive waves absorbers made of rolled up plastic nettings as shown in Picture 4 :
Wave Absorber
Picture 3: Electric Motor
Picture 4 : Wave Absorber
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di Genova7
The equipment for the measurement of
the forces is:
-3 load cells as shown in Picture 5:
Load Cell Setup
-2 data acquisition cards in order to
change the analogue value into digital
-1 analogue signal generator in order
to maintain a constant t during the
recording of the signal
-1 computer for data recording
The definition of the problem starts choosing:
-the typology of the structure
-the geometry of the platform
-the environmental conditions
Picture 5: Load Cell Setup
Picture 6 : Data Acquisition Equipment
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di Genova8
Typology of the structure
In order to exploit the traits
of the wave tank and theequipment at disposal we
decided to carry out fixed
body tests on a Semi-
submerged Quad-floater.
The model must be fixed to
the tank by an external
structure expressly built.
This kind of floating
system is anchored to the
seabed in reality with four
tension legs which mustremain in tension also when
the platform is in wave
trough, and preserve the
same distance as the
floating structure from the
bottom of the sea. Upper connections are semi-submerged in order to enhance the stability
with a larger inertia moment. Thus movements of heave, roll and pitch are blocked while
surge, sway and yaw are still present. The affinity between the degrees of freedom allowed
from the anchoring system and the nature of the measuring system permits us to assimilate
one to the other by approximation.
Tests will hive us only the wave load data, comprehensive of effects due to reflection on thewalls of the tank and the refraction on the body. They are the first step for a possible future
development as unfixed model tests.
Geometry of the platform
The main dimensions are determined by designing the semi-submerged platform which fits
the 3.6 MW wind turbine designed by General Electric and used for offshore plants. From
simple calculations about the GMT and the other Hydrodynamics requirements of theplatform, the following dimensions were decided taking into consideration the structural
requirements:
Overall length=L =36.25m
Overall width=W=36.25m
Main Cylinder Diameter = 7.5m
Main Cylinder Height= 20m
Stability Cylinder Diameter=9.0m
Stability Cylinder Height=7.6m
Connection Arm Diameter=3.4m
Connection Arm Length=12.9m=1150 t
Picture 7: Geometry of the Platform
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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V=1122 m3
ZB=10.6 m
ZG=34.55 m
x=1.34 m
Aw=380 m2
Iy=47046 m4
RT=41.1 m
GMt=15.81 m
Environmental conditions
According with the need to design a structure which sustain bad weather and rough seas, we
decided to consult a document of the BMT Argoss - Wave Climate in order to decide the
main features of the waves approaching the structure. Table 1:Stochastic Mediterranean SeaWave Data refers to the distribution of significant wave heights versus mean periods,
measured with SAR technique in which the direction of propagation is not measured. It is
interesting to note that the highest height values (Hs= 5.2 m --- 8 m) are related with the
highest values of the mean period (P=8 s --- 11s).
lower 1 2 3 4 5 6 7 8 9 10 11
lower upper 2 3 4 5 6 7 8 9 10 11 12 total
0.1 0 0.2 0 0.008 0.871 1.547 0.338 0.06 0.006 0 0 0 0 2.829
0.3 0.2 0.4 0 0 1.599 4.414 2.214 0.314 0.055 0 0 0 0 8.596
0.5 0.4 0.6 0 0.002 2.17 4.968 3.664 0.942 0.082 0.021 0 0 0 11.849
0.7 0.6 0.8 0 0.002 1.793 5.708 4.051 1.365 0.141 0.017 0.002 0 0 13.079
0.9 0.8 1 0 0 0.541 5.649 4.111 1.58 0.187 0.008 0 0 0 12.076
1.1 1 1.2 0 0 0.023 4.178 3.902 1.608 0.227 0.004 0 0 0 9.942
1.3 1.2 1.4 0 0 0 2.537 3.424 1.481 0.282 0.021 0 0 0 7.7451.5 1.4 1.6 0 0 0 1.15 3.676 1.414 0.371 0 .021 0 0 0 6.632
1.7 1.6 1.8 0 0 0 0.291 3 .403 1.42 0.398 0.015 0 0 0 5.528
1.9 1.8 2 0 0 0 0.023 2.526 1.466 0.392 0.03 0.002 0 0 4.439
2.1 2 2.2 0 0 0 0 1.559 1.747 0.36 0.053 0 0 0 3.719
2.3 2.2 2.4 0 0 0 0 0.699 1.987 0.377 0.072 0.004 0 0 3.139
2.5 2.4 2.6 0 0 0 0 0.2 1.612 0.402 0.074 0.004 0 0 2.292
2.7 2.6 2.8 0 0 0 0 0.051 1.252 0.4 0.076 0.004 0 0 1.784
2.9 2.8 3 0 0 0 0 0.004 0.836 0.506 0.08 0.011 0 0 1.437
3.1 3 3.2 0 0 0 0 0.002 0.51 0.533 0.076 0 .021 0 0 1.142
3.3 3.2 3.4 0 0 0 0 0 0.232 0.52 0.072 0.011 0 0 0.836
3.5 3.4 3.6 0 0 0 0 0 0.072 0.48 0.099 0.01 0 0 0.66
3.7 3.6 3.8 0 0 0 0 0 0.015 0.402 0.118 0.01 0 0 0.544
3.9 3.8 4 0 0 0 0 0 0.008 0.324 0.112 0.008 0 0 0.451
4.1 4 4.2 0 0 0 0 0 0 0.168 0.141 0.002 0 0 0.31
4.3 4.2 4.4 0 0 0 0 0 0 0.118 0.166 0.008 0 0 0.291
4.5 4.4 4.6 0 0 0 0 0 0 0.04 0.12 0.015 0 0 0.175
4.7 4.6 4.8 0 0 0 0 0 0 0.013 0.124 0.01 0 0 0.147
4.9 4.8 5 0 0 0 0 0 0 0.004 0.108 0.019 0 0 0.131
5.1 5 5.2 0 0 0 0 0 0 0.004 0.027 0.017 0 0 0.048
5.3 5.2 5.4 0 0 0 0 0 0 0 0.046 0.013 0 0 0.059
5.5 5.4 5.6 0 0 0 0 0 0 0 0.013 0.013 0 0 0.027
5.7 5.6 5.8 0 0 0 0 0 0 0 0.015 0.008 0 0 0.023
5.9 5.8 6 0 0 0 0 0 0 0 0.008 0.015 0 0 0.023
6.1 6 6.2 0 0 0 0 0 0 0 0.004 0.01 0 0 0.013
6.3 6.2 6.4 0 0 0 0 0 0 0 0 0.013 0 0 0.013
6.5 6.4 6.6 0 0 0 0 0 0 0 0 0.008 0 0 0.008
6.7 6.6 6.8 0 0 0 0 0 0 0 0 0.006 0.004 0 0.01
6.9 6.8 7 0 0 0 0 0 0 0 0 0 0 0 0
7.1 7 7.2 0 0 0 0 0 0 0 0 0 0 0 0
7.3 7.2 7.4 0 0 0 0 0 0 0 0 0.002 0 0 0.002
7.5 7.4 7.6 0 0 0 0 0 0 0 0 0 0.002 0 0.002
7.7 7.6 7.8 0 0 0 0 0 0 0 0 0 0.002 0 0.002
7.9 7.8 8 0 0 0 0 0 0 0 0 0 0 0 0
0 0.011 6.996 30.466 33.823 19.922 6.788 1.742 0.244 0.008 0 100
Percentage of occurrence of wave height (m) in rows versus mean wave period (s) in columns
total
Copyright ARGOSS, October 2010Table 1:Stochastic Mediterranean Sea Wave Data
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di Genova10
The wave length, according with the linear wave theory, for deep water condition is strictly
related with the wave period by the dispersion relation:
So the range of wave lengths will be:
Summarizing we will take cue from this data as to generate our waves both in the tank and in
the simulation software
2
2gT
=
mT
T
mT
T
1882
)(*81.911
1002
)(*81.98
22
22
2
111
===
===
mm
sTs
mHm
W
S
188100
118
82.5
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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MODEL CONSTRUCTION
Selection of Scale
From the main dimensions obtained and described in the previous chapter we need to define
a scale to represent the project we did with a model which has to fit into the wave tank. On
one hand we prefer to avoid by choosing a too big scale: it would mean small forces and an
accurate measurement would be very difficult; furthermore the representation of the physicalphenomena due to the fluid flow could be different from the reality. On the other hand
choosing a too small scale would invalidate our tests because of the small space around the
model, which would produce a great reflection phenomena of the waves on the tank walls.
Thus, according to the previous statements and considering the convenience of dealing with
an easy scale, we decide that the length scale will be:
Given the nature of the problem and the slow velocity of the water particles also when they
are on the wave crest, gravitational effects prevail over viscous ones. This predominance is
relevant enough for our model to be represented with the similitude of Froude and viscous
forces will be omitted.
According to the Similitude of Froude and considering the length scale stated we can write:
100
1==
R
M
L
L
where U is the velocity and a L a characteristic
length of the Model/Real objectM
M
M
R
RR
FrLg
U
Lg
UFr ===
**
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova12
Finally we can determine the force scale trough equalising the Newton numbers of the
platform and of the model:
The wave field will also be influenced by the same scale , thus we will consider this aspect atthe time of generating waves.
Given the length scale, we can easily obtain the model dimensions:
L =36.25cm
W=36.25cm
Main Cylinder Diameter = 7.6cm
Main Cylinder Height= 20cm
Stability Cylinder Diameter=9.0cm
Stability Cylinder Height=7.8cm
Connection Arm Diameter=3.4cm
Connection Arm Length=12.9cmV=1122 cm
3
==
===
==
===
R
M
M
R
RM
RM
R
M
R
RR
M
MM
R
M
R
M
R
M
T
T
T
T
LT
TL
U
U
T
LU
T
LU
L
L
gL
gL
U
U
**
*
;
*
*
where is the time scale10
1==
3
22
1
424
24
24
2424
)(***
*
**
=
===
===
R
M
RR
MM
R
M
R
RR
R
MM
MM
F
F
TL
TL
F
F
NwTL
F
TL
FNw
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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ZB=10.6 cm
Aw=380 m2
Iy=47046 m4
RT=41.1 m
Construction and junction materials
The material of construction are pipes of polypropylene (PP), easy to find in different
diameters and with good mechanical properties for machining. Its only problem is its smooth
surface, and because of this the PP has to be glued with a special bonder such as the
"LOCTITE 430 Super Bonder Instant Adhesive". It is a single component, general industrial
grade, cyanoacrylate adhesive with a low viscosity.
Machine working and assembly
Accurate workings can be done only by accurate machines and good technicians; in fact both
affect the precision of the work and represent the upper limit of the accuracy we can obtain.
The laboratory of the University of Malta is equipped with high precision machines, as
lathes, vertical drills and numerical control machine (NCM), but also with welding
equipment and all the necessary tools for working. The design of the model and all the other
components for the measurement of the forces has been discussed with the trained and
experienced workers of the University as to match our design with the needs of that working
procedure. Furthermore each machining had to be presented on its own drawing, approved bythe supervisor Eng. John Borg.
During the machining we found some difficulties with the PP. In fact the machines are made
to work with iron, steel and metal in general, so we had to reduce the velocity of machining
to decrease the heat due to friction and avoid melting the PP.
The assembly was initially made only with the bonder "LOCTITE 430 Super Bonder Instant
Adhesive" and using a sort of potting, a structure that was keeping the components blocked
and aligned on the right position. Then after a failed hardness test performed by the Prof.
Eng. Tonio Sant we decided to improve the model with few layers of fibreglass.
Construction tables and drawings are into the drawing appendix.
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
Platforms in Extreme Sea Conditions
Umberto Ghisaura - Universita degli Studi di Genova14
WAVE TANK
The first time we worked on the wave tank we focused on the features of the waves we were
able to generate and on their quality. As the tank was built for a different kind of
experiments, many problems has to be solved.
Wave Period
The swinging panel which generates the
waves is moved by an electric motor
equipped with an inverter that allows us
to modulate the frequency, and
consequently also the round per minute
of the shaft and the period of the waves.
The frequency, before our modification,
was adjustable from 0 to a maximum of
50 Hz, that corresponds to a wave period
of 0.6 seconds. Working on the setup
menu of the inverter, shown in Picture 8:
Electric Inverter for the Regulation of
the Wave Period, we allowed the
frequency of the motor to reach a
maximum value of 60 Hz which
corresponds to a wave period of 0.5 s.
Even if the motor was not designed toexceed the maximum of 50 Hz, we could
do it because of the small energy
required; in fact to a small period
corresponds a small wave and small load
energy and heat for the motor.
Furthermore we checked that the
amperage did not exceed the level
recommended by the producing
company.
Picture 8: Electric Inverter for the Regulation of the
Wave Period
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di Genova15
Wave Height
According to the linear wave theory1, the flux of energy transmitted by a cylindrical wave
through a plan is
)(cos)2sinh(
21
2
1 22tkx
kd
kd
kga
t
E
+=
It is interesting to remember that the time derivate of the energy is the Power.
If we want to find out the transmitted energy in one period we have to integrate the flux of
energy in the time T at the point x=0:
=
+=
+=
=
dtt
kd
kdcgadttkx
kd
kd
kga
t
EE
TT TT
)(cos)2sinh(
21
2
1)(cos
)2sinh(
21
2
1 2222
+=
+=
)2sinh(
21
4
1*
)2sinh(
21
4
1 22
kd
kdgaT
kd
kdcga
+=
)2sinh(
21
4
1 2
kd
kdgaE
T
The mean energy transmitted during a period T, which represent a power, is:
+=
+==
)2sinh(
21
4
1
)2sinh(
21
4
1 22
kd
kdcga
kd
kdga
TT
EE T
Furthermore the dispersion equation says
)(*2 kdtghgk= )(* kdtghgk=
thus the velocity )(*)(*
kdtgh
k
g
k
kdtghgk
k
c ===
where
a is the amplitude of the linear wave
T
2= is the frequency
T is the wave period
2=k is the wave number
1
Fenton, J.D. (1985). "A Fifth -order Stokes Theory for Steady Waves". J. Waterway, Port,Coastal and Ocean Eng., Vol.111.
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Experimental and Numerical Methods for the Evaluation of Wave Loads on Offshore
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Umberto Ghisaura - Universita degli Studi di Genova16
is wave lengthd is depth of the bottom
In deep water d
1)( kdtgh and 2)sinh(
1 +kd
kd
Thus we can rewrite both equations
22ggk==
2
*2 2
2
Tgg ==
2
* g
k
gc == cgaE 2
2
1=
The dispersion equation shows that the wave length is proportional to the square of the
period and the velocity is proportional to the square root of the wave length. This yields that,
in the linear wave theory in deep water condition, if we increase the mean transmitted
energy, keeping constant the rpm of the motor and consequently the wave period, only the
amplitude of the waves will increase. In our case, increasing the power at constant rpm
means extending the arm of the crankshaft and generate different higher waves. Thus it will
be useful to deal with an adjustable crank.
The preliminary test
we did during the
first attempt to the
wave tank showed
problems about the
oversized height of
the waves. This
because of the
excessive length of
the crank and its
scarse adjustability,
in fact there were
only 3 possible
regulation at 12, 24
and 36 centimetres
of length.
Picture 9: Initial Crank
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Thus we decided to improve
the wave generator with a
new adjustable rounded
shaped crank designed and
built by us in the University
of Malta. Now the generator
has 12 regulations of the
length of the crank at 2, 2.5,
3.2, 4, 5, 6, 7, 8, 9, 10, 11,
12 centimetres. The
accuracy of the distance of
the holes, which fits in the
connection rod, from the
rotation shaft is guaranteed
by the numerical control
machine.
Construction drawings are
attached to the thesis book.
Regularity and Turbulence of the waves
Since we are going to measure
the wave characteristics and the
acting forces on the model weneed to generate the more regular
and cylindrical waves than we
can. Considering the wave
height, if the wave was not
cylindrical for its whole width,
when we measured the height on
the tank wall we would find a
different value from the one in
the middle of the tank which runs
over the model. Furthermore it
would generate a transversaloscillatory movement and some
second order effects that we
cannot estimate.
Picture 10: New Circular Adjustable Crank
Picture 11: Initial Swin in Panel Setup
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The swinging panel was fixed in the
wave tank by an external support
with two coplanar upright. The
presence of these two elements on
the sides of the panel created two
vortices each half period which was
transported with the flow through the
whole tank. The presence of this
secondary flow self-generated by the
swinging panel would make us
miscalculate the forces, as we cannot
estimate the turbulence and its
effects on the floating structure. In
order to avoid this effect we decided
to change the geometry of the
support structure of the panelmoving backward the two uprights
and extending the swinging panel
close to the tank walls. The wave
generator is still fixed to the tank
through two horizontal rods placed
between the new uprights and the
base of the swinging panel.
Picture 12: New Swinging Panel Setup
Picture 13: Initial Waves with Turbolences
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Standing wave
One of the undesired disturbances of wave tanks which is most common and difficult toavoid is wave reflection from the tank end. It occurs when this generated wave on one side of
the tank is reflected on the opposite side and comes back. This undesired effect comes out by
the superposition of the reflected wave over the generated wave :
This formula describes a wave that oscillates in time, but has a spatial dependence that is
stationary: sin(kx). At locations x = 0, /2, , 3/2, ... called the nodes the amplitude is
always zero, whereas at locations x = /4, 3/4, 5/4, ... called the antinodes, the amplitude is
maximum. The distance between two conjugative nodes or anti-nodes is /2.
Open sea and ocean waves are generally represented with Stokes waves of order from 1 to 4,
so they are progressive, not stationary. It means that water particles change position at each
period T and the spatial dependence is not stationary. To avoid the reflection on the opposite
side of the tank, a wave absorber is commonly set up. It is possible to achieve good results
with one passive wave absorber whose length is the same length as the waves.
The wave absorber on the opposite side of the wave generator was built by cylinders made of
rolled-up plastic nettings. The waves flow through cylinders moving in the direction
)sin()cos(2
)sin()sin(
)sin(
)sin(
0
0021
02
01
kxtyy
tkxytkxyyyy
tkxyy
tkxyy
=
++=+=
=
+=
Picture 14: Example of Final Wave Generated
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perpendicular to the cylinder axis and the height goes on reducing both before and after the
reflection on the wall. The damping coefficient is related with the rate between the diameter
of the mesh of the netting and wave height; thus the smaller the wave height the thicker the
mesh has to be. To maintain this rate constant we have to reduce the diameter of the cylinder
and to thicken the netting as the waves flow through the absorber.
Even though the tank was equipped with a passive wave absorber some standing waves were
still present. The difference between the wave length which the absorber was designed for
and the length of the waves we decided to generate caused these disturbances. To avoid this
disturbances we implemented the absorber with 45 cylinders of a thicker mesh inserting them
into the sparse mesh cylinders.
Picture 16: Initial Wave Absorber
Picture 15: Final Wave Absorber
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WAVE SAMPLING
Generating Waves
First of all we need to prearrange all the equipment to measure, generate and video record the
waves. The frequency of the inverter is related with the frequency of the swinging panel so
we need a table in order to adjust the wave frequency working on the inverter.
Inverter
frequency
50 46 43 40 38 35.5 33.5 30 27.5 26.5
Wave
frequency
0.6 0.65 0.7 0.76 0.8 0.86 0.9 1 1.1 1.15
In order to measure the wave height and wave length we positioned on the side of the tank a
vertical rudder and a horizontal graduated stripe of paper adhesive tape, both of them
oriented with a plumb line. Thus, according to the range of periods and heights given by the
previous table, we started to generates waves. We will follow the same procedure for eachone of the generated waves: we set a length on the crank and a period on the inverter when
the water in the tank is calm. Each condition was recorded with a camera both the measuring
objects, and then we switched on the generator. The realized videos are essential in order to
measure the height of crest and trough and the length using a slow motion media player.
Unfortunately a wave probe was not available, so the wave measurements of the wave
characteristic was made visually during the test and on videos a posteriori.
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These surveys allowed us to produce a complete sampling of the wave tank using the circular
crank we built at different settings. Our purpose is to generate non-linear waves, such as 2nd
and 3rd order Stokes waves, to represent extreme sea conditions. This is the reason why we
will leave aside waves above 3 centimetres and with a small slope.
Period [s] 1.15 Motor Freq 26.5 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5
3.2
4
5
6
7
8 81.60 73.70 7.90 77.65 77.60 205.00 25.95 5.7E-02
9
Period [s] 1.1 Motor Freq 27.5 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5
3.2
4 80.20 76.50 3.70 78.35 78.25 188.00 50.81 0.06
5 81.00 76.00 5.00 78.50 78.25 189.00 37.80 0.06
6 81.45 75.60 5.85 78.53 78.25 190.00 32.48 0.067 82.25 75.05 7.20 78.65 78.25 190.00 26.39 0.06
8 82.90 74.30 8.60 78.60 78.25 191.00 22.21 6.3E-02
9
Picture 17: Sampling Waves
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Period [s] 1 Motor Freq 30 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5
3.2
4 80.95 75.90 5.05 78.43 78.25 157.00 31.09 0.08
5 81.80 75.30 6.50 78.55 78.25 160.00 24.62 0.08
6 82.45 75.05 7.40 78.75 78.25 162.00 21.89 0.087 83.10 74.40 8.60 78.75 78.25 164.00 19.07 0.08
8 83.60 73.90 9.70 78.75 78.25 165.00 17.01 7.5E-02
9
Period [s] 0.9 Motor Freq 33.5 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5
3.2
4 81.05 75.45 5.60 78.25 78.25 130.00 23.21 0.09
5 81.85 75.10 6.75 78.48 78.25 132.00 19.56 0.09
6 82.75 74.80 7.95 78.78 78.25 134.00 16.86 0.09
7 83.30 74.50 8.80 78.90 78.25 135.00 15.34 0.09
8 84.50 74.40 10.10 79.45 78.25 137.00 13.56 9.4E-02
9
Period [s] 0.86 Motor Freq 35.5 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5
3.2 79.65 75.90 3.75 77.78 77.60 113.00 30.13 0.10
4
5
6
7
8 84.70 74.00 10.70 79.35 78.25 125.00 11.68 1.0E-01
9
Period [s] 0.8 Motor Freq 38 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5 79.37 76.00 3.37 77.69 77.60 98.00 29.08 0.12
3.2 79.95 75.60 4.35 77.78 77.60 99.00 22.76 0.12
4 81.50 75.50 6.00 78.50 78.25 100.00 16.67 0.12
5 82.60 75.20 7.40 78.90 78.25 102.00 13.78 0.12
6 82.90 74.30 8.60 78.60 78.25 105.00 12.21 0.12
7 83.80 74.30 9.50 79.05 78.25 106.00 11.16 0.12
8
9
Period [s] 0.76 Motor Freq 40 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5 79.50 76.00 3.50 77.75 77.60 88.00 25.14 0.13
3.2 80.20 75.40 4.80 77.80 77.60 90.00 18.75 0.13
4
5 83.00 75.15 7.85 79.08 78.25 94.00 11.97 0.136 83.35 74.45 8.90 78.90 78.25 97.00 10.90 0.13
7
8
9
Period [s] 0.7 Motor Freq 43 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5 79.60 75.95 3.65 77.69 77.60 76.00 20.82 0.16
3.2 80.30 75.40 4.90 77.85 77.60 79.00 16.12 0.16
4 81.65 75.20 6.45 78.43 78.25 82.00 12.71 0.16
5
6
7
8
9
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Period [s] 0.65 Motor Freq 46.3 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5 79.65 75.85 3.80 77.75 77.60 68.00 17.89 0.18
3.2 80.80 75.50 5.30 78.15 77.60 70.00 13.21 0.18
4
5
67
8
9
Period [s] 0.6 Motor Freq 50 Hz
Crank amplitude [cm] Crest Height [cm] Trough Height [cm] H [cm] Mean Height [cm] Calm Water [cm] [cm] /H h/g*T^2
2
2.5 79.80 75.70 4.10 77.75 77.60 60.00 14.63 0.21
3.2
4
5
6
7
8
9
The surveys were carried out at least twice in order to avoid mistakes due to stochastic
effects. From these values we can obtain features such as the mean height and the values
2gT
hand
2gT
Hthat are essential to identify the effective order of the waves as it will be
shown later. Furthermore we added some further graphs to better understand how waves
parameters change with the wave period and to have a useful table for future experiments.
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Figure 1: Wave Theories Graph
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Figure 2: Generated Wave Order
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Figure 3: Wave Sampling - Wave Length vs. Period
WaveLength
40.0
0
60.0
0
80.0
0
100.0
0
120.0
0
140.0
0
160.0
0
180.0
0
200.0
0
220.0
0
240.0
00.5
0.6
0.7
0
.8
0.9
1
1.1
1.2
1.3
Period(s)
L(cm)
2.5cm
3.2cm
4cm
5cm
6cm
7cm
8cm
L
=g*T^2/6.28
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Figure 4: Wave Sampling - Wave Height vs. Period
WaveHeight
0.00
2.00
4.00
6.00
8.00
10.00
12.00
0.5
0.6
0.7
0.8
0.9
1
1.1
1.2
Period(s)
H(cm)
2.5cm
3.2cm
4cm
5cm
6cm
7cm
8cm
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Figure 5: Wave Sampling - H/L vs. Period
H/L
0.0
0
10.0
0
20.0
0
30.0
0
40.0
0
50.0
0
60.0
00.5
0.6
0.7
0.8
0.9
1
1.1
1.2
Period(s)
H/L
2.5cm
3.2cm
4cm
5cm
6cm
7cm
8cm
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Figure 6: Wave Sampling - Wave Height vs. Crank Length
Figure 1: Wave Theories Gh summarizes linear and non-linear wave theories dividing the
area of the chart in different zones through some lines defined by equations. The independent
2.00
3.00
4.00
5.00
6.00
7.00
8.00
9.00
10.00
11.00
2
3
4
5
6
7
8
9
Crank(cm)
Waveheight(cm)
0.65
0.7
0.76
0.8
0.9
1
1.1
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variable2
gT
h, which relates the depth h with the period T, is relevant to identify if the
seabed influences the wave shape, while the dependent variable2
gT
H, which relates the
wave height H with the period P, is related to the shape and to the slope of the wave.
Figure 2: Generated Wave Order
shows that our waves are both of the second and third order of Stokes and that points for
small periods are in the initial "transitional water" zone. This is a marginal problem, because
height and length are only slightly affected by the deepness by a mean 1.5%. Anyway, we
decide to do experimental tests for most of the points even though they are in the transitional
water area, while for the numerical testing we will take only those points marked with a
circle.
Figure 3: Wave Sampling - Wave Length vs. Period verifies the good quality of the generated
waves comparing them with the dispersion relation
2
* 2Tg= . We can ascertain that the
obtained wave length is coherent with theoretical values except for small a reasonable gap
due to measuring errors.
Figure 4: Wave Sampling - Wave Height vs. Period shows the little decreasing slope of the
value of the height at the change of the period, using the crank length as parameter.
Figure 5: Wave Sampling - H/L vs. Period is meant to be as advice while generating waves.It is important to monitor the slope in order to avoid the breaking waves and evaluate how
much more we can decrease the period while generating at constant crank length.
Figure 6: Wave Sampling - Wave Height vs. Crank Length confirms the theory we discussed
in the previous paragraph about the Wave Height. At equal period, there is an almost
proportional relation between the two variables.
Reading the exact wave order and the seabed deepness on the graph we can decide which
waves to use for experimental test and which for numerical ones.
Crank 0.6 s 0.65 s 0.7 s 0.76 s 0.8 s 0.86 s 0.9 s 1.0 s 1.1 s 1.15 s
2.5 cm exper not tested exper not tested exper and num --- --- --- --- ---
3.2 cm --- exper not tested exper exper and num exper --- --- --- ---
4.0 cm --- --- exper --- exper and num --- exper and num exper exper ---
5.0 cm --- --- --- exper exper and num --- exper and num exper exper ---
6.0 cm --- --- --- exper exper and num --- exper and num exper exper ---
7.0 cm --- --- --- --- exper and num --- exper and num exper and num exper ---
8.0 cm --- --- --- --- --- exper exper and num exper exper exper
Period
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Experimental Wave Profile Control
This verification wants to carry out a deeper analysis comparing the generated wave profile
with the theoretical profile developed by Fenton2
. From one frame of the video for themeasurement of the wave length we digitize the wave profile referring some points to a
couple of axis. For theoretical profiles, we reproduce the same wave with linear, second
order third order and fifth order Stokes waves, using the deepness, the wave height and the
wave length data already sampled .
Picture 18: Period 0.9 s Crank 4 cm Wave Profile Control Digitization - Second Order Stokes Wave
2
Fenton, J.D. (1990) "Non linear Waves Theories". The Sea,Vol.9, Wiley & Son Inc., NewYork.
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Picture 19: Period 1.0 s Crank 5 cm Wave Profile Control Digitization - Second Order Stokes Wave
Picture 20: Period 1.0 Crank 7 cm Wave Profile Control Digitaztion - Third Order Stokes Wave
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The theoretical model developed by Fenton3
for the second order waves uses the formula
below to define the profile :
)2cos(***cos** 22
1 bb fakfa +=
where
1bf =1
2bf =
h)*(ksinh*4
h))*cosh(2k(2*h)*cosh(k3
+
Fenton4
developed also a model for the third order Stokes waves:
)3cos(***)2cos(***cos** 332
2
2
1 bbb fakfakfa ++=
where
1bf and 2bf are those parameter explained above
3bf =
)*(sinh*64
)3)*(cosh*24(6
6
hk
hk +
For the fifth order wave, we decided to use the Skjelbreia-Hendrickson5
model.
=
=
5
1
* )cos(1
i
i ik
ak**1 =
24
4
22
2*
2
*)*(*)*( BakBak +=
35
5
33
3*
3 *)*(*)*( BakBak +=
3 - 4 Fenton, J.D. (1990) "Non linear Waves Theories". The Sea,Vol.9, Wiley & Son Inc., New
York.
Scarsi, G. (1998). "Onde di gravita` regolari". Collana di Idraulica, Marina Edizioni
Litograph, Genova.
5Skjelbreia, L. and Hendrickson, J.A. (1960). "Fifth order Gravity Wave Theory". Proc. 7th ICCE, Vol.1.
Scarsi, G. (1998). "Onde di gravita` regolari". Collana di Idraulica, Marina EdizioniLitograph, Genova.
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44
4*
4 *)*( Bak=
55
5*
5 *)*( Bak=
S=sinh(k*h)
C=cosh(k*h)
3
2
22S*4
1)C*C(2B
+=
9
2468
24S*384
21)C*322C*192-*504C*C(272B
++=
C
6
6
33S*64
1)C*(8*3B
+=
)1C*6(S*12288
81)-C*54C*6264C*21816C*54000*70848C*208224-C*(88128B
212
2468101214
35
+++=
C
)1C*6(S*384
21)-C*106C*48*48C*448-C*(768*CB
29
246810
44
++=
C
)3*11*8(*)1C*6(S*12288
225)C*1050C*1800C*7160C*7280*20160(
)3*11*8(*)1C*6(S*12288
)C*83680C*262720-C*(192000B
24210
246810
24210
121416
35
+
+++
+
+=
CC
C
CC
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Figure 7: Period 0.9 s Crank 4 cm Wave Profile Comparison
Figure 8: Period 1.0 s Crank 5 cm Wave Profile Comparison
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We choose these three waves in order to do three controls of the profile, referring to the
Figure 1: Wave Theories Graph, in points with a value of2*Tg
Hlargely different.
Except for few points, we can appreciate the good quality of the generated waves comparingthem to relative theoretical profile: the real crest is 1.16% lower than the wave amplitude
compared to the theoretical whereas the trough is coincident. Other minimal gaps are on the
body of the waves.
Even though our tank waves are only of second and third order we decided to add to the
graph the first and the fifth order profile to better evidence the order of magnitude of an
approximation we are doing. The RANSE solver we will use for the numerical simulations
can reproduce only linear and fifth order waves, so we have to choose one of these to
approximate our tank waves. The comparisons show the great difference between linear and
tank profile, and the close resemblance between the fifth and the other non-linear waves.
Figure 9: Period 0.9 Crank 7 cm Wave Profile Comparison
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LOAD CELLS AND DATA ACQUISITION
Load Cells
Each load cell we used, manufactured by the Laboratory of
the University of Malta, is made of a circular steel ring
with two screws placed on the external side, diametrically
opposed to each other. The measurement is done by fourstrain gauges linked with a full bridge connection and
glued with a special bonder to the ring. The strain gauge is
just a resistor which modifies its resistivity coefficient
with its deformation. The full bridge connection plans to
put the four sensors on the diameter perpendicular to the
direction of strain, two on each side, one internal and one
external and doing the mean of the values surveyed.
Placing the gauges in this way may help us to obtain better
data because of the mean error effect. So, the load applied
to the ring deforms the shape and consequently also the
strain gauges which register the phenomena and send the
analogical data to the acquisition system. Notice that the
load cells are sensible to every kind of strains they are
subjected to, so it is
important to build an
external structure with appropriate constrains in order to
make them work only in the axial direction. Load cells must
be calibrated imposing a known load and noting down the
value of the voltage, then you can draw the calibration
equation and evaluate the dispersion of the points from the
line. Furthermore, it is compulsory that the deformationremains into the
elastic range in
order to maintain
the most
obtainable linear
relation between
the strain and
voltage during the
calibration.
Picture 22: Load cells setup
Picture 21: Strain gauge
Picture 23: Full Bridge
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Calibration On-Site
The sensitivity of the load cells
does not allow us to do the
calibration and then mount the
equipment on the model, as there
would be pre-load effects and the
slope could change. The best way
to avoid data mistakes is doing our
calibration on-site: we mount all
the equipments and then we start
taking measurements. Furthermore,it is compulsory to do a calibration
each day we obtain the data and
wait some time when we turn on
the pc in order to warm up the
electric circuit: electric devices are
sensitive to temperature and they
do different measurement of the
same load if they are not working
in isothermal condition, reached
only after some half hours later than when they are just turned on.
The calibration consists in drawing a graphic by points, where the independent variable is theweight we impose and dependent variable is the voltage we read on the calibration software.
Then we find the trend line that relates the points and we check that points are on a straight
line by calculating the dispersion R. So, entering the equation of the calibration for each load
cell, when we will take the measurement we will read the force expressed in kilograms.
KLC1
y = 0.0011x - 0.0055
R2
= 0.9994
-0.006
-0.0055
-0.005
-0.0045
-0.004
-0.0035
-0.003
-0.5 0.0 0.5 1.0 1.5 2.0 2.5
Weight [Kg]
Voltage[V]
KLC1 Calibration Linear (KLC1 Calibration)
Figure 10: KLC1 Calibration
Picture 24: Calibration On-Site
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KLC2
y = 0.0012x + 0.014
R2
= 1
0.0135
0.014
0.0145
0.015
0.0155
0.016
0.0165
0.017
-0.5 0 0.5 1 1.5 2 2.5
Weight [Kg]
Voltage[V]
KLC2 Calibration Linear (KLC2 Calibration)
Figure 11: KLC2 Calibration
KLC3
y = 0.0017x - 0.0194
R2
= 0.9997
-0.02
-0.019
-0.018
-0.017
-0.016
-0.015
-0.014
-0.500000 0.000000 0.500000 1.000000 1.500000 2.000000 2.500000 3.000000
Weight [Kg]
Voltage[V]
KLC3 Calibration Linear (KLC3 Calibration)
Figure 12: KLC3 Calibration
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Data Acquisition System
The first electronic device where the signal of the strain gauges arrives is the data acquisition
card. Each card can process 2 signals with an amplifier and an ADC (Analog to DigitalConverter). The first one amplifies in order to avoid the noise due to the electric net of the
lab (such as neon lights in the room and the standard noise transmitted by other electrical).
The second one discretizes the signal at a constant time step, usually referring to the clock
rate of the pc. As we are dealing with waves with a minimum period of 0.6 seconds (1.67 Hz)
and we need to work with a minimum step of 10 points per half-period, our time step will be
t =snumberofpo
period
intmin
min= 0.6/20=0.03 second (33.3 Hz)
So we rounded down to t =0.025 seconds (40 Hz).
After few test we realized that the time step we were dealing with was too small for the pc
clock, the t is inconstant, so we had to enhance the current setup. The solution we found
was to add an analog signal generator which sends the input for the discretization in place of
the pc. Since the device can generate digital signals with different shapes till a maximum
frequency of 1000 Hz we verified the precision of the 40 Hz signal with "sawtooth test".
This test consists in emitting a sawtooth shaped signal with a frequency higher than the 40
Hz we need, such as 50 Hz like as we did. Then a plot of the points recorded with the data
acquisition system is prepared and the right position of the points and the shape of the
sawtooth is checked. The points must lay on the straight lines as the Figure 13: Sawtooth test
shows an exemple of this comparison.
Sawtooth
-1
-0.8
-0.6
-0.4
-0.2
0
0.2
0.4
0.6
0.8
1
30 30.2 30.4 30.6 30.8 31 31.2 31.4 31.6 31.8 32
Time [s]
Volts[V]
Sawtooth
Figure 13: Sawtooth test
After the ADC the digital signal is recorded with the software LabVIEW in a text file.
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System of axis
The system of axis which Forces will refer to is the one on the centre of buoyancy, where the
x-axis is opposite to the wave advancing direction, the z-axis is parallel to the direction of theforce of gravity with the negative side facing the seabed, and y-axis is perpendicular to the
previous two axis.
Geometry of the External Structure
The external structure is meant to rigidly sustain the model while satisfying the cinematic
conditions of blocked mode tests. As we decided to deal with symmetric body test problem
and carrying out this test for the first time we decided to evaluate only the forces on the x-z
plan: the force on the direction of the Surge, FX, the force on the direction of the Heave, FZ,and the moment on the direction of the Pitch, FY. Error! Reference source not found.
shows how we decided to arrange the layout of the load cells in order to measurement the
Forces. A hollowed aluminium rod is stacked inside the central cylinder and transfers the
forces to the three load cells. In order to measure only the normal force we decided to use
simply supported restraint. The load cell on the top of the model has its axis parallel to the
vertical axis and from now on it will be called KLC3. KLC3 measures only the vertical force
and we need to change only the sign because of the axis orientation:
Fz=-KLC3*g
The two load cells on the upper left side have the axis parallel with the X-axis and from now
on they will be called KLC2 (the upper) and KLC1 (the lower). The horizontal force and the
moment are strictly related with these two load cells by these relations:
Fx=(KLC2+KLC1)*g
My=(KLC1*Z1+KLC2*Z2)*g
where Z1 and Z2 are the distance of KLC1 and KLC2 from the centre of buoyancy.
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CONSERVATION LAWS OF FLUID FLOW
Governing equations of fluid flow
The governing equations of fluid flow represent two mathematical statements of the
conservation laws of physics.
The mass of a fluid is conserved.
The rate of change of momentum equals the sum of the forces on a fluid particle (Newton's
second law).
The fluid will be regarded as a continuum. For the analysis of fluid flows at macroscopic
length scales (say 1 m and larger) the molecular structure of matter and molecular motionsmay be ignored. We describe the behavior of the fluid in terms of macroscopic properties, suchas velocity, pressure, density and temperature, and their space and time derivatives. These may
be thought of as averages over suitably large numbers of molecules. A fluid particle or point
in a fluid is then the smallest possible element of fluid whose macroscopic properties are not
influenced by individual molecules.
We consider such a small element of fluid with sides x, y and z.
The six faces are labeledN, S, E, W, T, B which stands for North, South, East, West, Top and
Bottom. The positive directions along the co-ordinate axes are also given. The centre of the
element is located at position (x,y,z). A systematic account of changes in the mass, momentum
and energy of the fluid element due to fluid flow across its boundaries and, where appropriate,
due to the action of sources inside the element, leads to the fluid flow equations.
All fluid properties are functions of space and time so we would strictly need to writep(x,y,z,t),
p(x,y,z,t), T(x,y,z,t) and u(x,y,z,t) for the density, pressure, temperature and the velocity vector
respectively. To avoid unduly cumbersome notation we will not explicitly state the
dependence on space co-ordinates and time. For instance, the density at the centre (x,y,z) of a
fluid element at time tis denoted by and the x-derivative of, say, pressurep at (x,y,z) andtime tby p/x. This practice will also be followed for all other fluid properties.
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The element under consideration is so small that fluid properties at the faces can be
expressed accurately enough by means of the first two terms of a Taylor series expansion.
So, for example, the pressure at theEand Wfaces, which are both at a distance of1/2x fromthe element centre, can be expressed as
Mass conservation in three dimensions
The first step in the derivation of the mass conservation equation is to write down a mass
balance for the fluid element.
The rate of increase of mass in the fluid element is
Next we need to account for the mass flow rate across a face of the element which is given by
the product of density, area and the velocity component normal to the face. From the figure
beyond it can be seen that the net rate of flow of mass into the element across its boundaries
is given by
Flows which are directed into the element produce an increase of mass in the element and get
a positive sign and those flows that are leaving the element are given a negative sign.
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The rate of increase of mass inside the element is now equated to the net rate of flow of mass
into the element across its faces. All terms of the resulting mass balance are arranged on the
left hand side of the equals sign and the expression is divided by the element volume xyz.
This yields
or in more compact vector notation
For an incompressible fluid(i.e. a liquid) the densityis constant and equation becomes
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Rates of change following a fluid particle and for a
fluid element
The momentum and energy conservation laws make statements regarding the changes of
properties of a fluid particle. Each property of such a particle is a function of the position
(x,y,z) of the particle and time t. Let the value of a property per unit mass be denoted by . Thetotal or substantive derivative ofwith respect to time following a fluid particle, written as
D/Dt, is
A fluid particle follows the flow, so x/t = u, dy/dt= v and dz/dt = w. Hence the substantivederivative ofis given by
D/Dtdefines the rate of change of property per unit mass. As in the case of the massconservation equation we are interested in developing equations for rates of change per unit
volume. The rate of change of property per unit volume for a fluid particle is given by the
product ofD/Dtand density, hence
The mass conservation equation contains the mass per unit volume (i.e. the density ) as theconserved quantity. The sum of the rate of change of density and the convective term in the
mass conservation equation (2.4) for a fluid element is
The generalization of these terms for an arbitrary conserved property is
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Formula (2.9) expresses the rate of change ofper unit volume plus the net flow ofout ofthe fluid element per unit volume. It is now re-written to illustrate its relationship with the
substantive derivative of:
The term [/t + div(u)] is equal to zero by virtue of mass conservation (2.4). In words,relationship (2.10) states
To construct the three components of the momentum equation and the energy equation the
relevant entries for and their rates of change per unit volume as defined in (2.8) and (2.10)are given below:
Momentum equation in three dimensions
Newton's second lawstates that the rate of change of momentum of a fluid particle equals the
sum of the forces on the particle.
The rates of increase ofx-, y- andz- momentum per unit volume of a fluid particle are given
by
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We distinguish two types of forceson fluid particles:
surface forces
-pressure forces
-viscous forces
body forces
-gravity force
-centrifugal force
-Coriolis force
-electromagnetic force
It is common practice to highlight the contributions due to the surface forces as separate
terms in the momentum equation and to include the effects of body forces as source terms.
The state of stress of a fluid element is defined in terms of the pressure and the nine viscous
stress components. The pressure, a normal stress, is denoted by p. Viscous stresses are
denoted by . The usual suffix notationij , is applied to indicate the direction of the viscousstresses. The suffices i andj in ij indicate that the stress component acts in the j-direction on asurface normal to the i-direction.
First we consider the x-components of the forces due to pressurep and stress components xx,yx and zx shown in the figure above. The magnitude of a force resulting from a surface stressis the product of stress and area. Forces aligned with the direction of a co-ordinate axis get a
positive sign and those in the opposite direction a negative sign. The net force in the x-
direction is the sum of the force components acting in that direction on the fluid element.
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On the pair of faces (E, W) we have
The net force in the x-direction on the pair of faces (N,S) is
Finally the net force in the x-direction on faces TandB is given by
The total force per unit volume on the fluid due to these surface stresses is equal to the sum
of the above terms divided by the volume xyz:
Without considering the body forces in further detail their overall effect can be included by
denning a source Smx of x-momentum per unit volume per unit time.
The x-component of the momentum equation is found by setting the rate of change of x-
momentum of the fluid particle equal to the total force in the x-direction on the element due to
surface stresses plus the rate of increase of x-momentum due to sources:
It is not too difficult to verify that the y-component of the momentum equationis given by
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and the z-component of the momentum equation by
The effects of surface stresses are accounted for explicitly; the source terms SMX,SMyand SMZ
in (2.14a-c) include contributions due to body forces only. For example, the body force due to
gravity would be modeled by SMX= 0, S\fy = 0 and Smz = -pg-.
Navier-Stokes equations for a Newtonian fluid
The governing equations contain as further unknowns the viscous stress components ij. The
most useful forms of the conservation equations for fluid flows are obtained by introducing asuitable model for the viscous stresses ij. In many fluid flows the viscous stresses can beexpressed as functions of the local deformation rate (or strain rate). In three-dimensional
flows the local rate of deformation is composed of the linear deformation rate and the
volumetric deformation rate.
The rate of linear deformation of a fluid element has nine components in three dimensions,
six of which are independent in isotropic fluids (Schlichting, 1979). They are denoted by the
symbol ey. The suffix system is identical to that for stress components (see section 2.4).
There are three linear elongating deformation components:
There are also six shearing linear deformation components:
The volumetric deformation is given by
In a Newtonian fluid the viscous stresses are proportional to the rates of deformation. The
three-dimensional form of Newton's law of viscosity for compressible flows involves two
constants of proportionality: the (first) dynamic viscosity, , to relate stresses to linear
deformations, and the second viscosity, , to relate stresses to the volumetric deformation. Thenine viscous stress components, of which six are independent, are
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Not much is known about the second viscosity , because its effect is small in practice. For
gases a good working approximation can be obtained by taking the value =-2/3 (Schlichting, 1979). Liquids are incompressible so the mass conservation equation is div u=
0 and the viscous stresses are just twice the local rate of linear deformation times the
dynamic viscosity.Substitution of the above shear stresses (2.31) into (2.14a-c) yields the so-called Navier-
Stokes equations:
Often it is useful to re-arrange the viscous stress terms as follows:
The viscous stresses in they- and z-component equations can be re-cast in a similar manner.
We clearly intend to simplify the momentum equations by 'hiding' the two smallercontributions to the viscous stress terms in the momentum source. Denning a new source by
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the Navier-Stokes equations can be written in the most useful form for the development of
the finite volume method:
Conservative form of the governing equations of
fluid flow
To summarize the findings thus far we quote in the table beyond the conservative or
divergence form of the system of equations which governs the time-dependent three-
dimensional fluid flow
Differential and integral forms of the general
transport equations
It is clear from the previous table that there are significant commonalities between the
various equations. If we introduce a general variable the conservative form of all fluid flowequations, including equations for scalar quantities such as temperature and pollutant
concentration etc., can usefully be written in the following form
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In words
This equation is the so-called differential general transport equation for property . It clearly
highlights the various transport processes: the rate of change term and the convective term onthe left hand side and the diffusive term (T =diffusion coefficient) and the source term
respectively on the right hand side. In order to bring out the common features we have, of
course, had to hide the terms that are not shared between the equations in the source terms. Note
that equations can be made to work for the internal energy equation by changing i into Tby
means of an equation of state.
Furthermore this equation is used as the starting point for computational procedures in the
finite volume method. By setting equal to 1, u, v, w and i (or T or h0) and selectingappropriate values for the diffusion coefficient and source terms we obtain special forms ofthe summarizing table for each of the five partial differential equations for mass, momentum
and energy conservation.
The key step of the finite volume method is the integration of the differential general transport
equation over a three-dimensional control volume CVyielding:
The volume integrals in the second term on the left hand side, the convective term, and in the
first term on the right hand side, the diffusive term, are re-written as integrals over the entire
bounding surface of the control volume by using Gauss' divergence theorem. For a vector a
this theorem states
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Applying Gauss' divergence theorem, the integral equation can be written as follows:
A diffusive flux is positive in the direction of a negative gradient of the fluid property , i.e.
along direction -grad . For instance, heat is conducted in the direction of negative
temperature gradients. Thus, the product n (- grad) is the component of diffusion fluxalong the outward normal vector, and so out of the fluid element. Similarly, the product n (grad), which is also equal to (-n (- grad), can be interpreted as a positive diffusion fluxin the direction of the inward normal vector -n, i.e. into the fluid element.
The first term on the right hand side , the diffusive term, is thus associated with a flux into
the element and represents the net rate of increase of fluid property of the fluid element dueto diffusion. The final term on the right hand side of this equation gives the rate of increase ofproperty as a result of sources inside the fluid element.In words, this relationship for the fluid in the control volume can be expressed as follows:
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THE FINITE VOLUME METHOD
Now we develop the numerical method based on this integration, the finite volume (or control
volume) method, by considering the simplest transport process of all: pure diffusion in the
steady state. The governing equation of steady diffusion can easily be derived from the
general transport equation for property by deleting the transient and convective terms. Thisgives
The control volume integration, which forms the key step of the finite volume method that
distinguishes it from all other CFD techniques, yields the following form:
By working with the one-dimensional steady state diffusion equation the approximation
techniques that are needed to obtain the so-called discretized equations are introduced.
Consider the steady state diffusion of a property in a one-dimensional domain defined inthe figure beyond. The process is governed by
where T is the diffusion coefficient and Sis the source term. Boundary values ofat pointsA and B are prescribed. An example of this type of process, one-dimensional heat conduction
in a rod, is studied in detail in this section:
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Step 1: Grid generation
The first step in the finite volume method is to divide the domain into discrete control
volumes. Let us place a number of nodal points in the space between A and B. The boundaries(or faces) of control volumes are positioned mid-way between adjacent nodes. Thus each node
is surrounded by a control volume or cell. It is common practice to set up control volumes
near the edge of the domain in such a way that the physical boundaries coincide with the
control volume boundaries.
At this point it is appropriate to establish a system of notation that can be used in future
developments. The usual convention of CFD methods is shown in the figure above.
A general nodal point is identified by P and its neighbors in a one-dimensional geometry, the
nodes to the west and east, are identified by Wand Erespectively. The west side face of the
control volume is referred to by 'w' and the east side control volume face by V. The distances
between the nodes W and P, and between nodes P and E, are identified by xWP and xPE
respectively. Similarly the distances between face w and point P and between P and face e aredenoted by xwP and xPe respectively. Furthermore the figure above shows that the controlvolume width isx = xpe.
Step 2: Discretization
The key step of the finite volume method is the integration of the governing equation (or
equations) over a control volume to yield a discretized equation at its nodal point P. For the
control volume defined above this gives
HereA is the cross-sectional area of the control volume face, Vis the volume and is theaverage value of source Sover the control volume. It is a very attractive feature of the finite
volume method that the discretized equation has a clear physical interpretation. This equation
states that the diffusive flux ofleaving the east face minus the diffusive flux ofentering thewest face is equal to the generation of, i.e. it constitutes a balance equ