[8] investigation of the semi-dimple vortex generator applicable to, 2014.pdf
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Investigation of the semi-dimple vortex generator applicable to
n-and-tube heat exchangers
Chi-Chuan Wang a, *, Kuan-Yu Chen a , Yur-Tsai Lin b
a Department of Mechanical Engineering, National Chiao Tung University, Hsinchu 300, Taiwanb Department of Mechanical Engineering, Yuan Ze University, Taoyuan, Taiwan
a r t i c l e i n f o
Article history:
Received 17 June 2014
Received in revised form
14 September 2014
Accepted 20 September 2014
Available online xxx
Keywords:
Fin-and-tube heat exchanger
Semi-dimple
Vortex generator
Heat transfer
a b s t r a c t
The present study examines the air side performance of the n-and-tube heat exchangers having semi-
dimple vortex generator or plain n geometry. A total of eight samples are made and tested with the
correspondingn pitch (Fp) being 1.6 mm and 2.0 mm and the number of tube row (N) are 1 and 2. The
inlet air ow direction is also being tested upon the proposed semi-dimple VG. Test results indicate that
the heat transfer performance of the proposed semi-dimple VG with N 1 at a smaller n pitch of
1.6 mm is slightly higher than that of plain n geometry. ForN 1 with a larger n pitch of 2.0 mm, the
semi-dimple VG is about 10% higher than that of plain n geometry. The difference in heat transfer
performance amid VG and plain n geometry becomes more pronounced with N 2 and is especially
evident when Fp 2.0 mm due to mixing contribution. In general, the difference between plain and
semi-dimple geometry becomes more conspicuous at a larger n pitch because of the comparatively
effectively swirled motion. Both geometries show a dependence on n pitch at N 1 but the effect is
almost negligible when N is increased to 2. The inlet air ow direction casts negligible inuence on the
heat transfer performance of semi-dimple VG. However, the friction factors for the opposite air ow
operation is lower than that of normal operation, especially in low Reynolds number region.
2014 Elsevier Ltd. All rights reserved.
1. Introduction
In typical air-cooled heat exchanger applications, normally the
air-side thermal resistance accounted for nearly or more than 90%
of the total thermal resistance. Hence accommodation of large n
surface area is the generally adopted. In addition, protrusions or
interrupted surfaces can be mounted on at surfaces to provide
better heat transfer performance. The surfaces can be in the form of
continuous surfaces (e.g. plain, wavy) or interrupted (louver, slit,
offset, and the like). Some review articles by Wang [1,2] had
reviewed the patents of enhanced surfaces related to the
n-and-tube heat exchangers. From the 80 patents being surveyed, 90% of
them are related to the interrupted surfaces. However, interrupted
surface normally accompanied appreciable pressure drops.
Accordingly, one of the recent designs is to introduce the so-called
vortex generator (VG) which may ease the problem of signicant
pressure drop caused by highly interrupted surfaces. Through some
specic protrusions, e.g. wing or winglet-type vortex generators
with an angle of attack, desired heat transfer augmentation at the
expense of affordable increase in pressure drop can be achieved [3].
For VGs applicable to the air-cooled heat exchangers, the rst
investigation was done by Edwards and Alker[4]who showed that
the local heat transfer coefcient can be increased as much as 40%.
Fiebig et al. [5] reported the improvements in heat exchanger
performance by punching vortex generators on the primary heat
transfer surface. Tiggelbeck et al. [6,7]examined the inuence of
rectangular wing and delta winglet on the performance ofn-and-
tube heat exchanger. Their experimental results found that theinline arrangement is superior to staggered arrangement when VG
is applied.
Biswas et al.[8], and Fiebig et al.[9,10]numerically investigated
the inuences of geometrical congurations of VG such as rectan-
gular wing, triangular winglet and the corresponding geometry
parameters like aspect ratio and attack angle. They concluded that
an aspect ratio of 2 and an attack angle of 30 provides the best
ratio of heat transfer/pressure drop. For an inline arrangement,
55e65% heat transfer enhancement with moderate rise of pressure
drop of 20e45%. Wang et al. [11] conducted a water tunnel visu-
alization experiment by utilization of an enlarged scale wave type
* Corresponding author. EE474, 1001 University Road, Hsinchu 300, Taiwan.
Tel.: 886 3 5712121x55105; fax: 886 3 5720634.
E-mail addresses: [email protected], [email protected]
(C.-C. Wang).
Contents lists available atScienceDirect
Applied Thermal Engineering
j o u r n a l h o m e p a g e : w w w . e l s e v i e r . c o m/ l o c a t e / a p t h e r m e n g
http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054
1359-4311/
2014 Elsevier Ltd. All rights reserved.
Applied Thermal Engineering xxx (2014) 1e6
Please cite this article in press as: C.-C. Wang, et al., Investigation of the semi-dimple vortex generator applicable to n-and-tube heatexchangers, Applied Thermal Engineering (2014), http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054
mailto:[email protected]:[email protected]://www.sciencedirect.com/science/journal/13594311http://www.elsevier.com/locate/apthermenghttp://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054http://www.elsevier.com/locate/apthermenghttp://www.sciencedirect.com/science/journal/13594311mailto:[email protected]:[email protected] -
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VG applicable to n-and-tube heat exchanger. Their results clearly
indicated that introducing VGs greatly relief the futile transverse
vortices behind the tube.
There hadbeen numerousnumerical studies associated with the
performance of VG type n-and-tube heat exchangers[12e18], but
only very few studies had actually implemented VG in the actual
n-and-tube heat exchangers. For instance, He et al. [19] imple-
mented a triangular winglet VG in a n-and-tube heat exchanger
having inline conguration. Their experimental results show little
impact of the 10 array and a moderate heat-transfer improvement
up to 32% for the small pair, both introducing additional pressure
loss of approximately 20e40%. Wang et al.[20]compared air-side
performance between delta-winglet VGs and wavy-n surface in
n-and-tube heat exchangers under dry- and wet-surface condi-
tions. With the rise of tube row, they found that the performance of
the VG surface relative to the wavy-n surface becomes more
evident.
In this study, the authors propose an alternative VG congura-
tion that is based on the dimple design. With the presence of
dimple alongside the n surface, the ip side becomes a hemi-
sphere. As the air ow across the dimple surface, the ow separa-
tion may occur and it would generate a re-circulation zone and an
upwash ow. The upwash vortices periodically ow out the dimpleto give rise to horseshoe vortices and improved the heat transfer
process accordingly. Tests are then performed and are compared
with plain n geometry. In essence, the overall objective of this
study is therefore to present some detailed comparisons of the air
side performance of the semi-dimple VG against and plain n ge-
ometry. The effects of the n pitch and the number of tube row will
be also reported in this study.
2. Experimental setup
As tabulated inTable 1,a total of eight sample coils which in-
cludes plain and semi-dimple VG. The detailed dimension and the
photo of the semi-dimple VG is schematically shown in Fig. 1.
Notice that the n thickness (df), collar diameter (dc), transverse
pitch (Pt), and longitudinal pitch (Pl) for all the test samples are
0.11 mm, 7.5 mm, 21 mm, and 18.2 mm, respectively. The corre-
spondingn pitch (Fp) rangesfrom1.6 to2.0 mm and the number of
tube row (N) spans from 1 to 2 as shown inTable 1.Detailed con-
struction of the circuitry arrangement is identical to Wang et al.
[21]. The experiments are conducted in an open wind tunnel as
shown inFig. 2. The ambient air ow was forced across the test
section by means of a 5.6 kW centrifugal fan with an inverter. To
avoid and minimize the effect of ow maldistribution in the ex-
periments, an air straightener-equalizer and a mixer were pro-
vided. The inlet and the exit temperatures across the sample coil
were measured by two T-type thermocouple meshes. The inlet
measuring mesh consists of twelve thermocouples while the outlet
mesh contains 36 thermocouples. The sensor locations inside therectangular duct were established following ASHRAE recommen-
dation [22]. These data signals were individually recorded and then
averaged. During the isothermal test, the variance of these ther-
mocouples was within 0.2 C.
The pressure drop of the test coil was detected by a precision
differential pressure transducer, reading to 0.1 Pa. The air ow
measuring station was a multiple nozzle code tester based on the
ASHRAE 41.2 standard[23]. The working medium in the tube side
was hot water. The inlet water temperature was controlled by a
thermostat reservoir having an adjustable capacity up to 25 kW.
Both the inlet and outlet temperatures were measured by two pre-
calibrated RTDs (Resistance temperature device, Pt-100 U). Their
accuracy was within 0.05 C. The water volumetric ow rate is
detected by a magnetic ow meter with 0.002 L/s resolution.
All the data signals are collected and converted by a data acqui-
sition system (a hybrid recorder). The data acquisition system then
transmitted the converted signals through GPIB interface to the host
computer for further operation. During the experiments, the water
inlet temperature was held constant at 60.0 0.2 C, and the tube
side Reynolds number was approximately 38,000. Frontal velocities
of inlet air ranged from 1 to 5 m/s. The energy balance between air
side and tube side was within 2%. The water side resistance (evalu-
ated as 1/hiAi) was less than 10% of the overall resistance in all cases.
The test n-and-tube heat exchangers are tension wrapped having
an Ltype n collar. Thermal contact conductance provided by themanufacturers ranged from 11,000 to 16,000 W/m2 K.
3. Data reduction
The -NTUmethod is applied to determine the UA product in the
analysis heat transfer and pressure loss characteristics of the test
coil from the experimental data. The detailed derivation of the heat
transfer coefcient can be referred to Wang et al.[21]and will not
repeat here. The obtained air sider heat transfer coefcient is then
in terms of the Colburnj factor:
j ho
rVmaxCpaPr2=3 (1)
whereVmax Vfr/s. The term,s, is the ratio of the minimum ow
area to frontal area. All the uid properties are evaluated at the
average values of the inlet and outlet temperatures under the
steady state condition. The friction factors are calculated from the
pressure drop equation proposed by Kays and London [24]. The
relation for the dimensionless friction factor,f, in terms of pressure
drop is shown below:
fAcAo
rm
r1
"2DPr1
G2c
1 s2
r1
r2 1
# (2)
whereAoandAcstand for the total surface area and the ow cross-
sectional area, respectively. Uncertainties in the reported experi-
mental values were estimated by the method suggested by Moffat
[25]. The derived uncertainties of Colburn jfactors range from 2.4 %
to 7.3 % and is 3.6% to 11.2 % of the friction factors.
4. Results and discussion
The test samples areof plain and semi-dimple VG congurations
with the number of tube row being 1, and 2. The corresponding n
pitches (Fp) are 1.6 and 2.0 mm, respectively. Test results are in
terms ofj and ffactors.Fig. 3denotes the test results for N 1 for
plain and semi-dimple VG geometry. For N1, it appears that thej
andfsemi-dimple VG is higher than those of the plain n geometry.
The Colburnjfactors for VG surface is about 10% higher than that of
plain surface when Fp is1.6 mmandRedc>
1000 but shows 20e
40%
Table 1
Detailed geometric parameters of the test samples.
No. Fp(mm) N, row Geometry
1 1.6 1 Plain
2 1.6 1 VG
3 2.0 1 Plain
4 2.0 1 VG
5 1.6 2 Plain
6 1.6 2 VG
7 2.0 2 Plain
8 2.0 2 VG
C.-C. Wang et al. / Applied Thermal Engineering xxx (2014) 1e62
Please cite this article in press as: C.-C. Wang, et al., Investigation of the semi-dimple vortex generator applicable to n-and-tube heatexchangers, Applied Thermal Engineering (2014), http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054
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higher friction factor. This is also applicable when Fp is raised to
2.0 mm. Both n geometries show a dependence ofn pitch when
N 1, and normally a smaller n pitch will lead to a higher heat
transfer performance. The effect ofn pitch on heat transfer per-
formance for N 1 is associated with the development of boundary
layer. Based on the experiments carried out by Saboya and Sparrow
[26]who used a naphthalene sublimating method, they found that
the boundary layer development for plain n geometry was the
most important factor of the 1-row n-and-tube heat exchanger,
and the effect of vortex might gain more importance as the Rey-
nolds number increased. Note that the results with respect to the
n pitch for plain n geometry is especially pronounced for N 1.
The subsequent results have shown that the difference in heat
transfer coefcient in association with n pitch is comparatively
small whenN2. The phenomenon can be further explained from
the numerical results of the effect ofn pitch carried out by Tor-
ikoshi et al.[27]. They conducted a 3-D numerical investigation of a
1-row plain n-and-tube heat exchanger. Their investigation
showed that the vortex forms behind the tube were suppressed and
the entire ow region was kept steady and laminar when the n
pitch was small enough. A further increase ofn pitch would result
in a noticeable increase of cross-stream width of vortex region
behind the tube. As a result, lower heat transfer performance is
seen for a larger Fp at a low frontal velocity when N 1. A recent
numerical simulation by Zhang et al.[28]of the n-and-tube heat
exchanger having plain n conguration also unveils similar re-
sults. Their simulation indicates that the steady state velocity elds
are reached when the n pitch is in the order of 2 mm (or less than
2.0 mm). On the other hand, when the n pitch is larger than 2 mm
but smaller than 12.38 mm, velocities exhibit some degree of os-
cillations. Despite the serious velocity oscillations, stable and
symmetric vortices are formed behind each tube and the duct ow
effect is more dominant, thereby deteriorating the heat transfer
performance. Note that the semi-dimple VG shows moderate heat
transfer improvement (~10%) over plain n geometry for N 1
whenFp2.0 mm. However, the improvement is reduced when Fpis reduced to 1.6 mm. In fact, the heat transfer improvement is only
1e5% when Redc is less than 1000. The results are actually not so
surprising due to several possible causes. Firstly, the entrance
length for the present plate n geometry is about 10 mm, impli-
cating improvement at the entrance region is comparatively futile.
Secondly, for the 1-row conguration, the generated vortices in the
rear part of the heat exchanger will impose less inuence on the
downstream area. Moreover, it becomes more apparent when the
n pitch is reduced for smaller n spacing will jeopardize the for-
mation of longitudinal vortices.
Fig. 1. Detailed geometry and photo of the semi-dimple VG and relevant operation (unit: mm).
C.-C. Wang et al. / Applied Thermal Engineering xxx (2014) 1e6 3
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Test results for N 2 are shown in Fig. 4. Asshownin the gures,
a further increase of the number of tube row (N 2), the air ow
within the plain n-and-tube heat exchanger may become periodic
developed, and results in the vortex-controlled regime. Conse-
quently, the effect ofn pitch on heat transfer performance is muchless profound for N 2. The results can be elaborated from the
numerical results of 2-row conguration by Torikoshi and Xi[29].
Their simulations show that the air ow after the rst row cylinder
is stabilized due tothe existence of the second tube row rather than
in the wake of the rst row. Therefore, the 2-row n-and-tube heat
10 Settling Devices (Flow Straightener)
7 T/C outlet temperature measuring station
5 T/C inlet temperature measuring station
3-phase, 220V
6 Test unit(Heat Exchanger)
3 Developing section
4 Pressure tap(inlet)
8 Pressure tap(outlet)
11 Nozzle pressure tap(inlet)
T
9 Mixer
PID
1 Air inlet2 Straightener
SCR
HEATER
ReservoirThermostatHot Water
Air Flow
13 Multiple nozzles plate
21 Temperature sensor
14 Settling Devices (Flow Straightener)
19 RTD inlet temperature of water side20 RTD outlet temperature of water side
12 Nozzle pressure tap(outlet)
17 Water pump
18 Water flow meter
22 Inverter
Hybrid
Recorder
15 Centrifugal fan16 Air discharge
Computer
GPIBPC
P H.X
SATP
NOZZLEP
3-phase, 220V
Fig. 2. Schematic of the test facilities.
N=1
Redc
100 1000 10000
f
dna
j
0.01
0.1
Fp = 1.6 mm (Plate)
Fp = 1.6 mm (VG)
Fp = 2.0 mm (Plate)
Fp = 2.0 mm (VG)
f
j
Fig. 3. Test results for N
1.
N=2
Redc
100 1000 10000
f
dnaj
0.01
0.1
Fp = 1.6 mm (Plate)
Fp = 1.6 mm (VG)
Fp = 2.0 mm (Plate)
Fp = 2.0 mm (VG)
f
j
Fig. 4. Test results for N
2.
C.-C. Wang et al. / Applied Thermal Engineering xxx (2014) 1e64
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exchanger still reveals similar results as those ofN 1. However, it
can be seen that the effect ofn pitch for N 2 become less pro-
found when compared with N 1. Apparently, this is because the
presence of additional staggered tube row that brings about better
mixing. In this regard, one can see that the effect of n pitch is
rather small, and this is applicable for both plain and semi-dimple
VG geometry. For the 2-row heat exchangers, it appears that the
heat transfer performance for the semi-dimple VG relative to plain
n geometry is increased. For instance, forFp2.0 mm, the j factor
for the semi-dimple VG geometry exceeds those of plain n
conguration by more than 17% when Redc is above 3000. The
corresponding increase of friction factoris about 30%. There are two
explanations for the rise of relative heat transfer performance be-
tween the semi-dimple VG and plain n. Firstly, the presence of
staggered tube row arrangement will bring about a better ow
mixing mechanism, and this mechanism is reinforced by the semi-
dimple. This can be made clear from the present semi-dimple ge-
ometry which features a punched open area below the semi-
dimple as depicted inFig. 1.Note that prior to manufacturing the
semi-dimple vortex generator n die, a separate numerical simu-
lation is carried out to determine the suitable location and the
arrangement of the semi-dimple vortex generator. Through the
punched open area, part of the air ow may ow through andyields a better mixing. As a consequence, the mixing mechanism
becomes more pronounced when the Reynolds number is
increased, thereby resulting in a detectable difference in heat
transfer performance amid plain and semi-dimple VG.
The previous studies[30,31]for plain n geometry also showed
that at a higher Reynolds number subject to a larger number of tube
row may also bring about vortices along the ns, therefore the effect
of n pitch on heat transfer coefcient is reduced. As depicted in
Fig. 4(N 2), one can see that the heat transfer performance of the
semi-dimple VG is almost independent ofn pitch. This is because
additional mixing augmentation caused by the staggered tube row is
imposed upon the swirled motion. The combined effects result in a
similar heat transfer performance for bothn pitches.
For comparison purpose, the air ow into the semi-dimple VGcan be reversed as shown inFig. 1(c). For normal operation, the air
ow encounters the semi-dimple VG which provides the protrusion
to generate vortices. For opposite operation, the air ow is directed
through the punched open area of the semi-dimple VG to provide air
ow mixing. Fig.5 shows the corresponding test resultsfor N 2 and
Fp 2.0 mm subject to normal and opposite air ow operations.
Interestingly, the heat transfer performance is barely the same while
the friction factor for the opposite operation is notably lower than
those of normal operation. The difference is especially pronounced
when theReynolds number is lower than 1500. In fact, thedifference
can be as high as 30e40%. The identical heat transfer performance
implies that the contribution of swirled ow and mixing mechanism
are actually comparable. The lower friction factor for opposite
operation is mainly associated of the airow being directed throughthe punched holes while under normal operation the air ow im-
pinges upon the semi-dimpledirectly, thereby a higher frictionfactor
for normal operation is encountered.
Based on the present test results, the heat transfer and frictional
performance of the proposed semi-dimple vortex generator can be
empirically correlated as:
j 0:29Re0:58dc
Fpdc
0:8N0:2 (3)
f2:2Re0:38dc 2Fpdc
0:5
1:4 log10RedcFpdc
1:5
! (4)
The foregoing equations can predict 90% of the measured semi-
dimple VG data within 10%.
5. Conclusions
In this study, an experimental study is carried out to examine
the air side performance of the n-and-tube heat exchangershaving plain or semi-dimple vortex generator. A total of eight
samples are made and tested in a well controlled wind tunnel. The
corresponding n pitch of the test samples are 1.6 mm and 2.0 mm
respectively and the number of tube row are 1 and 2, respectively.
The operational Reynolds number is from 400 to 4000. The inlet air
ow direction into the semi-dimple VG is also examined in this
study. Based on the foregoing discussions, some major conclusions
of this study are summarized as follows:
(1) For the air side performance for N 1 with a smaller n pitch
of 1.6 mm, the heat transfer performance for the semi-
dimple VG is slightly higher than that of plain n geome-
try. For a larger n pitch of 2.0 mm, the heat transfer per-
formance for the semi-dimple VG is approximately 10%higher than that plain n geometry but accompanies a
30e40% increase of friction factor.
(2) For the air side performance ofN 2, the effect ofn pitch
cast a negligible inuence on the heat transfer performance
for both n geometries. However, the heat transfer perfor-
mance of the semi-dimple VG relative to plain n geometry
is also increasing due to the contribution of mixing. A heat
transfer augmentation of 17% for semi-dimple VG can be
achieved but the corresponding friction factor penalty is
about 30%. The difference in heat transfer performance is
increased with the rising Reynolds number and the results
prevail for both n pitches. However, the difference in heat
transfer performance becomes more pronounced at a larger
n pitch due to comparatively effectively swirled motion.
N=2
Redc
100 1000 10000
f
dnaj
0.01
0.1
Fp = 2.0 mm (Normal VG)
Fp = 2.0 mm (Opposite VG)
f
j
Fig. 5. Comparison of the present semi-dimple VG subject to reversing inlet ow
condition.
C.-C. Wang et al. / Applied Thermal Engineering xxx (2014) 1e6 5
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(3) With regard to the effect of inlet air ow into the semi-
dimple VG heat exchangers, test results indicate that the
heat transfer performance is barely the same while the
friction factor for the opposite operation is notably lower
than those of normal operation. The difference is especially
pronounced when the Reynolds number is lower than 1500.
In fact, the difference can be as high as 30e40% when the
Reynolds number is less than 1000. The identical heat
transfer performance implies that the contribution of swirled
ow and mixing mechanism are actually comparable.
(4) A correlation is proposed to describe the data of semi-dimple
VG n-and-tube heat exchanger, the proposed correlation
can describe 90% of the test data within 10%.
Acknowledgements
The authors appreciate the nancial support from the Ministry
of Science and Technology, Taiwan under contract 103-3113-E-009-
002.
Nomenclature
A areaAc minimum ow area, rAfrAo total surface area
cp specic heat at constant pressure
dc n collar outside diameter,do 2dfdo tube outside diameter
f friction factor
Fp n pitch
Gc mass ux of the air based on the minimum ow
area,rVmaxho heat transfer coefcient
j Nu/RePr1/3, the Colburn factor
k thermal conductivity
N number of tube row
NTU number of transfer unitDP pressure drop
Pl longitudinal tube pitch
Pr Prandtl number
Pt transverse tube pitch
Redc rVdc/m, Reynolds number
T temperature
df n thickness
U overall heat transfer coefcient
Vfr frontal velocity
Vmax maximum velocity inside the heat exchanger, VmaxVfr/s
_Qave=
_Qmax, heat exchanger effectiveness
m dynamic viscosity ofuid
r density
s contraction ratio of cross-sectional area
Subscripts
1 air side inlet
2 air side outlet
air air side
f n surface
m mean value
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C.-C. Wang et al. / Applied Thermal Engineering xxx (2014) 1e66
Please cite this article in press as: C.-C. Wang, et al., Investigation of the semi-dimple vortex generator applicable to n-and-tube heatexchangers, Applied Thermal Engineering (2014), http://dx.doi.org/10.1016/j.applthermaleng.2014.09.054
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