Chemical Engineering Science 66 (2011) 2616–2626
Contents lists available at ScienceDirect
Chemical Engineering Science
journal homepage: www.elsevier.com/locate/ces
Twin jets in cross-flow
V.S. Naik-Nimbalkar a, A.D. Suryawanshi a, A.W. Patwardhan a,n, I. Banerjee b,
G. Padmakumar b, G. Vaidyanathan b
a
Department of Chemical Engineering, Institute of Chemical Technology, Matunga, Mumbai 400019, India
Experimental Thermal Hydraulics Section, Separation Technology and Hydraulics Division, Fast Reactor Technology Group, Indira Gandhi Centre for Atomic Research, Kalpakkam
603102, India
b
a r t i c l e i n f o
a b s t r a c t
Article history:
Received 13 January 2011
Received in revised form
4 March 2011
Accepted 9 March 2011
Available online 16 March 2011
An experimental study and numerical investigation of thermal mixing are carried out on tandem twin
jets in cross flow. Experiments were carried out for velocity ratios 1, 2 and 4 for 15 1C temperature
difference between main pipe and jet fluid. Velocity and temperature fields are measured using Hot
Film Anemometer (HFA). Three dimensional steady state Computational Fluid Dynamics (CFD)
simulations have been carried out to predict the velocity and temperature fields. The predicted velocity
and temperature fields are in good agreement with the experimental measurements. Temperature
fluctuations have been predicted using temperature variance model. The effect of jet spacing for
different velocity ratios is studied. For jet spacing equal to twice the jet diameter, both the jets influence
each other. Increase in the jet spacing decreases the effect of jets on each other.
& 2011 Elsevier Ltd. All rights reserved.
Keywords:
Mixing
Heat transfer
Fluid mechanics
Turbulence
CFD
Temperature fluctuations
1. Introduction
Jets in cross flow (JICF) are used in several engineering
applications related to heat and mass transfer. Single, twin and
multiple jets are introduced within the cross flow according to the
aim of the handled application. Twin and multiple jet configurations are found in combustor wall cooling, cooling of gas turbine
blades, etc. In these applications more than one jet is used to
enhance the performance of each individual jet further downstream of its injection point. Similarly, we find these types of jets
in the dispersion of hot liquid effluents into streams and rivers,
which is relevant to water pollution. Also, mixing elements in
static mixers and burners in the combustion units have rows of
multiple jets issuing in the cross flow fluid.
In literature several researchers have investigated single and
multiple jets in cross flow configuration. The twin jet configuration is significantly less considered in spite of its great relevance.
In fact, its understanding is likely to predict the effectiveness or
ineffectiveness of multiple jet systems. The existing work on
multiple jets focuses mainly on global characteristics such as jet
trajectory, vorticity and circulation aspects of multiple jets in
cross flow by varying number of jets in a row, or considering
specific geometrical configurations of jets (Ziegler and Wooler,
n
Corresponding author. Tel.: þ91 22 33612018; fax: þ 91 22 33611020.
E-mail address: aw.patwardhan@ictmumbai.edu.in (A.W. Patwardhan).
0009-2509/$ - see front matter & 2011 Elsevier Ltd. All rights reserved.
doi:10.1016/j.ces.2011.03.018
1971; Makihata and Miyai, 1979; Isaac and Jakubowski, 1985;
Kolar et al., 2003, 2006; Kolar and Savory, 2007; Radhouane et al.,
2009). The scalar mixing characteristics such as concentration,
temperature decay and temperature fluctuations that occur due
to thermal mixing have not been studied. Scalar mixing studies
are useful in solving design related issues. The present work
addresses thermal mixing issues in dual jet systems.
2. Previous work
The literature on the twin jets in cross flow (TJICF) is relatively
scarce. It was first studied by Ziegler and Wooler (1971) by means
of an analytical model for the flow of jets in cross flow. Different
multiple jet configurations were investigated and the influence of
an upstream jet on downstream jet was studied. The jet spacing
was three times diameter of jet. The second jet trajectory was
influenced by first jet as it was restricting the cross flow. The
analytical model predictions matched well with the experimental
data.
Makihata and Miyai (1979) described the experiments and
theoretical predictions of the trajectories of multiple buoyant and
non-buoyant jets. They employed a finite difference method of
analysis of momentum integral equation. The ratio of jet velocity
to cross flow velocity was maintained in the range 1.2–10.6. The
jets were emitted at an inclination angle of 451 and placed at a jet
spacing of 0.8d. Their theoretical predictions of jet trajectories and
V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
are illustrated by the flow visualization images. It showed that the
trajectories in tandem cases are higher than for single jet case.
Also dispersion aspects of twin jets were discussed using concentration measurements.
Radhouane et al. (2009) studied the interaction of twin tandem
in-line jets of variable temperature with cross flow. Particle image
velocimetry (PIV) was carried out on twin jets with 3d jet spacing,
1.29 velocity ratio and jet inclination of 601 with horizontal plane.
Numerical analysis was carried out using turbulent Reynolds stress
model (RSM). They have studied the temperature distribution by
tracking the evolution of the tangential shear stress component
along the domain. They concluded that the initial stream wise
inclination angle highly affects the thermal field that results from
the interaction of twin tandem jets emitted within the cross flow.
The main emphasis of the previous work was study of vorticity
characteristics of tandem twin jet systems. For tandem twin jet
systems, only few papers showed effect of upstream jet on second
jet and vice versa. Also scalar mixing characteristics of twin jets in
terms of concentration or temperature decay, temperature fluctuations that occur due to thermal mixing of hot twin jets in
cooler cross flow were not addressed. These were the objectives
of the present work.
diffusion characteristics of multiple jets were in close agreement
with the experimental data.
Isaac and Jakubowski (1985) carried out wind tunnel experiments
on different twin jet configurations. Hot wire anemometer was used
for the velocity field measurements. The results showed flow
similarities (mean velocity and turbulence parameters) between
the single jet and tandem (in-line) twin jets in the downstream
region of x/d410.
Kolar et al. (2003) experimentally studied the vorticity distribution and turbulent vorticity transport associated with the TJICF.
Velocity field measurements are carried out using hot wire anemometer. The vorticity transport features are visualized and interpreted in terms of turbulent vorticity fluxes. They have compared
tandem and side by side twin jet arrangements (5d spacing between
jets in both cases) in terms of vorticity distribution and jet penetration ability. They concluded that the above properties are strongly
dependant on geometrical parameters like jet spacing and the angle
between jet center to center connecting line.
Ibrahim and Gutmark (2006) investigated the effect of velocity
ratio ‘r’ on the dynamics of single and twin jet arrangement using
particle image velocimetry (PIV). They have studied jet trajectories and penetration, deflection, mass entrainment, windward
and leeward spread, decay rate and turbulent kinetic energy. In
tandem setup, trajectory and penetration of the second jet are
found to increase due to shielding effect of the upstream jet. Also,
the presence of upstream jet hindered the entrainment characteristics of the second jet. The windward and leeward spread of
the second jet was reduced by the presence of upstream jet. The
reverse flow confined between the upstream jet and second jet
was stronger than that of single jet and caused reduction in
the size of reverse flow region downstream of the second jet. The
peak turbulent kinetic energy value along the trajectory of the
second jet was 20% smaller than that of first jet. They attributed
the decrease in turbulent kinetic energy to the reduction in local
interaction between cross flow and second jet.
Kolar et al. (2006) investigated the vorticity distribution and
overall circulation associated with the vortical structure of the
TJICF. They have carried out wind tunnel experiments on single,
tandem, side by side and oblique jet (second jet was in-line with
upstream jet at 451) arrangements. Velocity field was measured
with hot film anemometry. They found that the vortical structure
of TJICF was similar to CVP (counter rotating vortex pair) of the
single jet in cross flow.
Kolar and Savory (2007) carried out velocity field analysis in
wind tunnel experiments. The similarities and differences
between the mean flow vortical features, vorticity and circulation
associated with three basic jet arrangements – tandem, side by
side and oblique – have been studied using hot wire anemometry.
The comparison with single jet case was also carried out. The
turbulent structures associated with the single and tandem jets
3. Cross flow type mixing experiments
Figs. 1 and 2 show tandem twin jet test section and schematic
diagram of experimental setup for cross flow experiments,
respectively (Naik-Nimbalkar et al., 2010). The different locations
of the second jet are 2 times jet diameter (2d), 4d and 6d from the
center of the first jet as shown in Fig. 1. T-junction of both jets
with cross flow pipe is constructed of acrylic pipes. Horizontal
main pipe is of 0.05 m inner diameter and T-junction branch pipe
is of 0.015 m inner diameter. Cold water enters from main pipe
and hot water from the branch pipe. Velocity ratios of 1, 2 and
4 were maintained between branch pipe and main pipe flow.
Table 1 shows the various experimental conditions maintained.
Temperature difference of 15 1C is maintained between water
from main pipe and jet with the help of temperature controllers
connected to thermocouples. Velocity ratios of 1, 2 and 4 were
maintained by adjusting flow-rate through main pipe and branch
pipe. Magnetic turbine flow-meters are employed to monitor
water flow-rate through main pipe and branch. The second
branch pipe is adjustable to set up 2d, 4d and 6d spacing between
centers of two jets. Velocity and temperature for both the branch
pipes were maintained same for each test run. Velocities and
temperatures at the main and branch pipes were confirmed to be
at steady-state before each experiment was performed.
Velocity and temperature measurements are carried out at
four locations as shown in Fig. 1 using Hot-wire anemometer
HFA measurement
locations
D
0.6m
y
Cold water in
(303 K)
1 2 3 4
x
1st Jet
Main pipe
Branch Pipe
(0.05m id, 1.2m long)
(0.015m id)
2617
nd
d
2d 4d 6d
Hot water in
(318 K)
2 Jet locations
Branch Pipe
(0.015m id)
Fig. 1. Tandem twin jet test section for cross flow experiments.
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
Temperature controllers
Main pipe
0.05m diameter
1.2m length
Water in
(303K)
TC1
To H1 To H2
To TC1
Thermocouple
HFA measurement
TC2
locations
1 2
3 4
Branch pipe
0.015 m diameter
Water in
(318K)
To TC2
Thermocouples
To Heat
Exchanger
Flow
meter
Flow
meter
From Heat
Exchanger
318K
303K
Heater
H2
H1
Fig. 2. Schematic diagram of experimental setup for twin jet in cross flow experiments.
Table 1
Experimental conditions for cross flow experiments.
Velocity ratio,
r ¼ Vh/Vc
1
2
4
Main pipe
Branch pipe (Both jets)
Diameter (m)
Velocity ‘Vc’ (m/s)
Temperature ‘Tc’ (K)
Diameter (m)
Velocity ‘Vh’ (m/s)
Temperature ‘Th’ (K)
0.05
0.05
0.05
0.5
0.5
0.33
303
303
303
0.015
0.015
0.015
0.5
1
1.32
318
318
318
(Streamline Research Anemometer System 90N10 Frame, Dantec
Dynamics Ltd., Denmark). HFA probe with support is mounted
using leak proof Swagelok fittings to facilitate smooth vertical
movement of probe. A constant temperature module (CTA) has
been used for the measurement of local velocity in the system.
The output of voltage versus time data was converted to velocity
versus time data using calibration with non-intrusive flow velocity elucidates from Laser Doppler Anemometer (LDA, Dantec
Dynamics Ltd., Denmark).
A constant current module (CCA) has been used for the
measurement of the local temperature in the system, which gives
output as voltage versus time data. The voltage versus time data
was converted to temperature versus time data with the help of
calibration using thermometer. Dual (55R63) X-film type of fiber
probe (quartz fiber probe covered by Ni thin film of thickness
0.1 mm, sensor diameter 70 mm, overall fiber length 3 mm, sensor
length 1.25 mm) has been used along with the standard probe
support provided with the system. At each measurement point,
sampling time was 4 s and sampling rate was 1000 samples
per second.
At first, cross wire point of HFA probe is fixed at the measurement location. The flows through the main and branch pipe are
started. The total outflow after mixing is passed though heat
exchanger and sent back to cold water tank. After achieving
steady state, HFA measurements were carried out for velocity
and temperature. For each measurement point same procedure is
repeated.
Figs. 3 and 4 show experimental measurements of X-velocity
and mean temperature respectively. 2d spacing twin jet measurements are compared with single jet in cross flow. Uncertainty
analysis was carried out by repeating experiments for several
times. There was þ/ 3% deviation in the measured values from
mean value of all the measurements. Error bars show the possible
range of variation in the experimental measurements in Figs. 3
and 4. From both the figures it is clear that the percentage error of
3% do not have any significant effect on velocity and temperature
field measurements. Fig. 3 shows X-velocity distribution for 2d
spacing twin jet at line 2 which is at 3d from first jet center. Line
2 is just after the entry of the second jet in cross flow. The single
jet measurements were carried out by making first jet off and
then the second jet was acting as single jet in cross flow. Fig. 3
shows X-velocity distribution for velocity ratio 4. For r ¼4, jet has
fairly large momentum and it practically impinges on the opposite wall. For single jet case, the sudden change in velocity near
the main pipe axis indicates the interaction point between jet
fluid and main pipe fluid. For 2d twin jet case, this point is above
the single jet case since the second jet penetrates more in the
main pipe fluid due to shielding effect of the first jet. First jet
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
0.5 m
0.4 m
y
Zone 1
0.05 m
Zone 2
0.3 m
Zone 3
x
0.015m
Fig. 5. Computational domain for 3-D CFD simulations.
((x, y) ¼(0, 0)) shown in Fig. 5 is on the centerline of the main pipe
above the 1st jet entry. Main pipe cold fluid flows downstream
along x-direction and jet fluid enters perpendicular to main pipe
axis along y-direction. To avoid entrance and exit effects, sufficient pipe length of 12D is maintained before and after 1st jet. The
end effects have been studied for single jet in cross flow in our
previous work Naik-Nimbalkar et al. (2010). The transport equations are as follows.
Mass conservation equation
Fig. 3. X-velocity distribution for 2d spacing twin jet on line 2 (3d) for r¼ 4 (m
Single jet experiments, ~ Twin jet experiments).
Momentum conservation equation
ð2Þ
0.8
Energy conservation equation
!
"
#
@T
@
W @T
at þ t
uj
¼
@xj
@xj
Prt @xj
0.6
0.4
Y / Rm
ð1Þ
@
@P
@
@ui @uj
@
þ
þ
ðrui uj Þ ¼
m
þ
rui 0 uj 0 þ rg bðT T0 Þ
@xj
@xi
@xj
@xi
@xj
@xj
1
0.2
0
-0.2
@ðrui Þ
¼0
@xi
0
0.2
0.4
0.6
0.8
-0.4
1
3d
y
x
-0.6
-0.8
d
2d
1Tm Normalized
Fig. 4. Mean temperature distribution for 2d spacing twin jet on line 2 (3d) for
r ¼4. Legend same as Fig. 3.
obstructs the cross flow and due to this second jet was not confronted with the actual cross flow velocity. The negative X-velocity
shows the recirculation zone near to the jet entry.
Fig. 4 shows the mean temperature distribution and comparison of 2d twin jet case with single jet in cross flow. As the jet
fluid was hot, normalized mean temperature varies from 1 to 0.
The sudden variation of the mean temperature denotes the
mixing region of jet and main pipe fluid as seen in Fig. 4. Peak
of the mean temperature for 2d spacing twin jet case is higher
than single jet case. This shows that due to shielding effect of first
jet, second jet penetrates more in the cross flow. The detailed
discussion of spacing effect on thermal mixing is continued along
with numerical results in the results and discussion section.
4. CFD simulations
Steady-state 3-dimensional CFD simulations were carried
out on the domain shown in the Fig. 5. The co-ordinate system
ð3Þ
Along with these transport equations, scalar transport equation for temperature variance was solved to predict temperature
fluctuation intensity. It was derived from basic thermal energy
equation and given as
pffiffiffiffiffiffiffi!2
!
"
#
!
@T 0 2
@
k2 @T 0 2
@T
@ T 02
0
ui
p þ CTT
¼
2ui0 T
2eT 0 2a
@xi
@xi
@xi
e @xi
@xi
ð4Þ
For solving temperature variance equation in CFD simulations,
we have to model some terms as follows. The right hand terms
are: molecular and turbulent diffusion, and gradient production,
dissipation for temperature variance and molecular dissipation,
respectively.
We have
eT 0 ¼
eT 02
ð5Þ
Rk
From gradient assumption of Fourier
u0i T 0 ¼ at
@T
@xi
ð6Þ
Using all the above modeled terms and neglecting molecular
dissipation, the temperature variance equation for steady state is,
!
"
#
!2
@T02
@
k2 @T02
@T
e
ui
¼
p þCTT
2at
2
T02
ð7Þ
@xi
@xi
@xi
e @xi
Rk
The ability of temperature variance equation to predict temperature fluctuation depends largely on the modeling of the
production and dissipation term. In previous literature, various
mathematical models are proposed for the modeling of dissipation term. The detailed analysis of prediction of temperature
fluctuations using different temperature variance models for
single jet in cross flow is carried out by Naik-Nimbalkar et al.
(2010). On the basis of that work, constant ‘R’ model (R¼2) is
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
used to predict temperature fluctuations in the present case of
twin jet in cross flow.
The transport equations have been solved using the FLUENT
software version 6.3.26 by Finite Volume Method. The standard
k e turbulence model was used. No slip and adiabatic condition
was given to the wall. Boundary conditions at inlet for this model
were mass flow inlet using the experimental conditions given in
Table 1. The outlet boundary condition was outflow. The variation
in density of working fluid due to temperature change was considered using the Boussinesq approximation and included as the
last term in Eq. (2).
ðrr0 Þg r0 bðTT0 Þg
ð8Þ
The transport equations for momentum, k and e were discretized using second order upwind scheme and the transport
equations for energy and T 02 were discretized using first order
upwind scheme. The pressure values at the faces were interpolated using the standard scheme and the transport equations are
solved using the SIMPLE algorithm. The equations were considered to be converged when the absolute values of the residuals
were below 1 10 4.
5.2. CFD model predictions
5.2.1. Prediction of X-velocity
Fig. 7 shows x-velocity contours for single jet and 2d, 4d, 6d
twin jet cases. Figs. 8–10 and show X-velocity distribution and
comparison of different twin jet cases with single jet in cross flow
for velocity ratio 4. X-velocity is normalized by the main pipe
velocity ‘Vc’. Fig. 8 shows X-velocity distribution for 2d spacing
twin jet at line 2, which is at 3d from first jet center. Line 2 is just
after the entry of the second jet in cross flow. For comparison the
single jet measurements were carried out by making first jet off
and then the second jet was acting as single jet in cross flow. Fig. 8
shows X-velocity distribution for velocity ratio 4. For r ¼4, jet
has fairly large momentum and it practically impinges on the
5. Results and discussion
5.1. Grid independency
Zone 2 in Fig. 5 was meshed with fine tetrahedral mesh of
2 mm (0.6 million), 1.5 mm (1.7 million) and 1.25 mm (1.92
million). Zones 1 and 3 were meshed with variable size tetrahedral mesh with size ratio of 1.2 and up to maximum size of
3 mm. Fig. 6 shows the CFD predictions of mean temperature on
the measurement line 2, which is at 3d from the coordinate
system as shown in Fig. 1. Mean temperature was normalized as
TmNormalized ¼
ðTTc Þ
ðTh Tc Þ
ð9Þ
From Fig. 6 it is clear that CFD predictions with 1.5 mm grid
size in zone 2 shows good match with the experimental data.
Further refinement of grid up to 1.25 mm in zone 2, does not
show significant improvement. Thus, grid size of 1.5 mm was
used in the zone 2.
1
0.8
3d
y
x
0.6
d
0.4
2d
Y / Rm
0.2
0
-0.2
0
0.2
0.4
0.6
0.8
1
-0.4
-0.6
-0.8
-1
Tm Normalized
Fig. 6. Grid independency: Mean temperature prediction for 2d spacing jet for
r¼ 1 at line 2 (3d). (m Experiments, ?? CFD simulations: zone 2–1.25 mm,
——— CFD simulations: zone 2–1.5 mm, - - - - - - - CFD simulations: zone
2–2 mm).
Fig. 7. X-velocity contours for r¼ 2. (a) Single jet, (b) 2d spacing twin jet, (c) 4d
spacing twin jet and (d). 6d spacing twin jet.
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
1
0.8
0.6
0.2
0
-1
-0.5-0.2 0
0.5
1
1.5
-0.4
2
2.5
3
3d
y
x
-0.6
d
-0.8
2d
-1
X-velocity Normalized
Fig. 8. X-velocity distribution for 2d spacing twin jet on line 2 (3d) for r ¼4
(m Single jet experiments, ~ Twin jet experiments, ——— Single jet CFD
simulations, - - - - - - - Twin jet CFD simulations).
1
0.8
0.6
Y / Rm
0.4
0.2
0
-0.5 -0.2 0
0.5
1
1.5
2
2.5
3
5.5d
-0.4
y
x
-0.6
d
-0.8
4d
-1
X-velocity Normalized
Y / Rm
Fig. 9. X-velocity distribution for 4d spacing twin jet on line 3 (5.5d) for r ¼4.
Legend same as Fig. 8.
5.2.2. Prediction of mean temperature
Figs. 11–13 and show the mean temperature distribution and
comparison of different twin jet cases with single jet in cross flow.
As the jet fluid was hot, normalized mean temperature varies
from 1 to 0. The sudden variation of the mean temperature
denotes the mixing region of jet and main pipe fluid as seen in
Fig. 11. In the recirculation zone as described in Figs. 7(b) and 8,
some of the cross flow fluid mixes with the jet fluid. So the mean
temperature decreases in that zone. This has also happened in the
case of 4d and 6d spacing cases as shown in Figs. 12 and 13.
Peak of the mean temperature for 2d spacing twin jet case is
higher than single jet case. This shows that due to shielding effect
of first jet, second jet penetrates more in the cross flow. With
increase in jet spacing, shielding effect decreases. So that the peak
difference for the 4d and 6d spacing case decreases as shown in
Figs. 12 and 13. In the twin jet cases, the thermal energy input
from jet fluid is double compared to single jet case. For 4d and 6d
cases, hot jet fluid mixes with the cross flow, which further
interacts with the second jet. So that mean temperature values
for twin jet cases are higher than single jet cases as shown in
Figs. 11–13. In above cases CFD model predictions of X-velocity and
mean temperature matches reasonably well with the experimental
1
1
0.8
0.8
0.6
0.6
0.4
0.4
0.2
0.2
0
-0.5 -0.2 0
0.5
1
1.5
2
2.5
3
8d
-0.4
y
Y / Rm
Y / Rm
0.4
opposite wall. For single jet case, the sudden change in velocity
near the main pipe axis indicates the interaction point between
jet fluid and main pipe fluid. For 2d twin jet case, this point is
above the single jet case since the second jet penetrates more in
the main pipe fluid due to shielding effect of the first jet. First jet
obstructs the cross flow and due to this second jet was not
confronted with the actual cross flow velocity. The contour plot
7(b) portrays this interaction of 2d spacing twin jet with cross
flow. The negative X-velocity shows the recirculation zone near to
the jet entry.
For the jet spacing of 4d and 6d, first jet gets fairly mixed with
the cross flow fluid. So that the cross flow has recovered its
momentum before interacting with the second jet. For r ¼4, the
first jet mixing with cross flow is improved and cross flow totally
overcome the shielding effect. Fig. 9 shows X-velocity distribution
for r ¼4 at line 3 (5.5d). Due to decrease in shielding effect of first
jet, the difference in the X-velocity distribution for single jet case
and 4d spacing case decreases. For 6d spacing case, the shielding
effect of first jet is almost removed as seen in Fig. 10. The contour
plots 7(c) and (d) show the decrease in shielding effect of first jet
with increase in the jet spacing.
0
-0.2 0
0.2
0.4
0.6
0.8
-0.4
-0.8
-1
x
-0.6
-0.6
d
d
-0.8
6d
X-velocityNormalized
Fig. 10. X-velocity distribution for 6d spacing twin jet on line 4 (8d) for r ¼4.
Legend same as Fig. 8.
3d
y
x
1
2d
-1
TmeanNormalized
Fig. 11. Mean temperature distribution for 2d spacing twin jet on line 2 (3d) for
r¼ 4. Legend same as Fig. 8
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
1
2
1.8
0.6
1.6
0.4
1.4
0.2
1.2
Y/rd
Y / Rm
0.8
0
-0.2 0
0.2
0.4
0.6
0.8
1
0.8
5.5d
-0.4
0.6
y
x
-0.6
0.4
0.2
d
-0.8
1
0
4d
1-
0
TmeanNormalized
Fig. 12. Mean temperature distribution for 4d spacing twin jet on line 3 (5.5d) for
r¼ 4. Legend same as Fig. 8.
0.5
1
X/rd
1.5
2
1
0.9
1
0.8
0.8
0.7
0.6
Y/rd
0.6
0.4
0.5
0.4
Y/Rm
0.2
0.3
0
-0.2 0
0.2
0.2
0.4
0.6
0.8
1
-0.4
0
x
0
-0.6
-0.8
-1
0.1
8d
y
0.2
0.4
0.6
0.8
1
X/rd
d
6d
TmeanNormalized
Fig. 13. Mean temperature distribution for 6d spacing twin jet on line 4 (8d) for
r¼ 4. Legend same as Fig. 8.
measurements. This validated CFD model is used for the prediction
of jet trajectory, centerline X-velocity decay, vorticity and temperature fluctuation intensity.
5.2.3. Prediction of jet trajectory
Fig. 14 shows Comparison of jet trajectories for single and first
jet of 2d, 4d, 6d spacing jets. The jet center is at (0, 0). For velocity
ratio 2, first jet trajectories for all the cases are identical as seen in
Fig. 10(a). Also trajectory data for r ¼3 given by Ibrahim and
Gutmark (2006) is plotted in Fig. 14(a). In their case, first jet
penetrates more in the cross flow fluid as shown in Fig. 14(a).
They have attributed the impact on the first jet to the fact that the
upward force of the restricted fluid between the two jets slows
down the rate of deflection of the first jet. The jet diameter to
main pipe diameter ratio in case of Ibrahim and Gutmark (2006)
is 0.08. The mass of the jet fluid and its momentum was lower
compared to main pipe fluid. So that it experiences the push from
restricted fluid between two jets. In the cases studied in the
present work, jet diameter to main pipe diameter ratio is 0.3. The
mass of the jet fluid and its momentum is comparable to cross
flow fluid. So that the effect on first jet similar to Ibrahim and
Gutmark (2006) cannot be seen.
Fig. 14. Comparison of jet trajectories for single and ‘first’ jet of 2d, 4d, 6d spacing
jets. (a). For r ¼ 2 (m Ibrahim and Gutmark (2006) single jet experiments, r ¼3. ~
Ibrahim and Gutmark (2006) Twin jet experiments J ¼3.55d, r¼ 3. ——— Single jet
CFD simulations. - - - - - 2d spacing twin jet CFD simulations. - - - - - - - 4d
spacing twin jet CFD simulations. ??? 6d spacing twin jet CFD simulations).
(b). For r ¼4 (——— Single jet CFD simulations. - - - - - 2d spacing twin jet CFD
simulations. - - - - - - - 4d spacing twin jet CFD simulations. ??? 6d spacing
twin jet CFD simulations).
Interestingly in the present study as the velocity ratio increases
to 4, trajectory of first jet for 2d spacing case is slightly lower than
single, 4d and 6d spacing case as seen in Fig. 14(b). The second jet in
2d spacing case pulling the fluid behind it due to pressure difference
and the first jet is close to that region. So that first jet slightly gets
pulled by second jet and its trajectory gets lower. Figs. 16 and 17
show gage pressure contours. For 2d spacing case, Figs. 16(a) and
17(a) show negative gage pressure zone in between the two jets.
The increase in velocity ratio results in the increase in low pressure
zone as seen in Fig. 17(a) and the pulling of the first jet as seen in
Fig. 14(b). As the jet spacing becomes 4d, first jet started mixing
with cross flow and the cross flow fluid flowing around the first jet
overcomes the low pressure zone. This can be seen from contour
plot Figs. 16(b) and 17(b).
In 2d twin jet case, first jet obstructs the cross flow fluid. Due
to this, second jet gets shielded from the cross flow fluid and
penetrates more in the main pipe as seen in Fig. 15. The shielding
effect can be clearly seen in Fig. 15(a) for velocity ratio 2 and in
Fig. 15(b) for velocity ratio 4. For 4d spacing case, second jet is at
more downward distance. Now first jet started mixing with cross
flow as seen in contour plot Fig. 7(c). Due to decrease in shielding
V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
2623
400
2
1.8
100
1.6
1.4
-300
Y/rd
1.2
-600
1
0.8
-900
0.6
-1200
(pa)
0.4
0.2
0
400
0
0.5
1
X/rd
1.5
2
100
1
-300
0.9
0.8
-600
0.7
-900
Y/rd
0.6
0.5
-1200
(pa)
0.4
0.3
Fig. 16. Gage pressure contour for r¼ 2. (a) 2d spacing twin jet. (b) 4d spacing
twin jet.
0.2
0.1
400
0
0
0.2
0.4
0.6
0.8
1
X/rd
Fig. 15. Comparison of jet trajectories for single and ‘second’ jet of 2d, 4d, 6d
spacing jets. (a) For r ¼2. Legend same as Fig. 14(a). (b) For r ¼4. Legend same as
Fig. 14(b).
100
-300
-600
effect, second jet penetration becomes lower and its trajectory
appears nearer to single jet case. For 6d spacing there is negligible
shielding effect of first jet on second especially for r ¼4. Ibrahim
and Gutmark (2006) observed the same shielding effect of first jet
on second jet for the 3.55d spacing twin jet case as plotted in
Fig. 15(a). From Figs. 14 and 15, it is clear that for jet spacing more
than 4d, the above mentioned effects of twin jets on each other
reduces.
-900
-1200
(pa)
400
100
5.2.4. Centerline X-velocity decay
Fig. 18 depicts the centerline X-velocity decay for r ¼2. The
centerline X-velocity decay for single and first jet of twin jet cases
is plotted in Fig. 18(a). For Ibrahim and Gutmark (2006) twin jet
case, first jet decay is more than single jet. In the case of present
study, first jet decay of 4d and 6d spacing case is similar to single
jet case since the twin jet interaction with each other becomes
lower. For 2d spacing case, the slight pulling by second jet and
low pressure zone between two jets causes faster decay of first jet
as seen in Fig. 18(a). For Ibrahim and Gutmark (2006) and present
study, the second jet decays slowly than the single jet as seen in
Fig. 18(b). Due to shielding effect of first jet on second, the second
jet carries its momentum longer than single jet. So that its
spreading is less and less amount of cross flow fluid can be
entrained by it. As a result second jet decay is lower than
single jet.
-300
-600
-900
-1200
(pa)
Fig. 17. Gage pressure contour for r¼ 4. (a) 2d spacing twin jet. (b) 4d spacing
twin jet.
5.2.5. Prediction of vorticity
The formation and decay of dominant vortical structure, the
counter rotating vortex pair (CVP), is closely associated with the
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
1
1
0.8
0.95
Y / rd
X-velocity / Vhmax
0.9
0.85
0.6
0.4
0.8
0.75
0.2
0.7
0
0.65
0
0.2
0.6
0.4
0.6
0.8
1
X / rd
0
0.5
1
1.5
2
2.5
Fig. 19. Y-locations of peak vorticity regions for r¼ 4. (–m– Single jet, –~–2d
spacing twin jet, –’– 4d spacing twin jet, –K– 6d spacing twin jet).
Y/d
1
1
0.95
0.8
0.6
0.85
0.4
0.8
0.2
Y / Rm
X-velocity / Vhmax
0.9
0.75
0.7
0
-0.2 0
0.1
0.2
0.3
-0.4
0.65
-0.6
0.6
-0.8
0
1
2
3
4
5
y
x
d
2d
-1
Y/d
0.4
3d
TrmsNormalized
Fig. 18. Centerline X-velocity decay for r¼2. (a) For single and 1st jet of twin jet cases.
Legend same as Fig. 14(a). (b) For single and 2nd jet of twin jet cases. Legend same as
Fig. 14(b).
1
0.8
0.6
0.4
Y / Rm
centerline turbulent vorticity transport across the plane of symmetry (Kolar et al., 2003). In the case of twin jets in cross flow, the
vortical structure is naturally more complex than for a single jet in
cross flow. The twin jet CVP is a result of merging process of the
stronger CVP of first jet with slightly weaker CVP of a downstream
shielded second jet. The second jet has higher transverse penetration
ability and having a lifting effect on resulting CVP. In the case of twin
jets, dominant vortical structures are formed downstream as a result
of merging process of vortical structures associated with two single
jets. Fig. 19 shows the center plane Y-locations of peak vorticity
regions in the downstream direction for single and twin jet cases.
Vorticity peaks for 2d spacing twin jets clearly show the shielding
effect of first jet on second. Due to higher transverse penetration of
second jet, vorticity peaks for 2d spacing twin jet case are higher
than single jet case. Kolar et al. (2003, 2007) have observed the same
trend of higher vorticity peak locations for twin jet case than single
jet case. As a result of increase in jet spacing, there is decrease in
shielding effect of first jet on second. For 4d spacing twin jet case,
peak vorticity regions are nearer to those of single jet case. In case of
6d spacing twin jets, peak vorticity locations are almost similar to
that of single jet case. This shows that the increase in jet spacing
decreases the interaction between two jets.
0.2
0
-0.2 0
0.1
0.2
0.3
-0.4
y
x
-0.6
-0.8
0.4
3d
d
2d
-1
TrmsNormalized
Fig. 20. Temperature fluctuation intensity distribution for 2d spacing twin jet on
line 2 (3d). (a) For r ¼2 (m Single jet experiments, ~ Twin jet experiments, ———
Single jet CFD simulations, ??? Twin jet CFD simulations). (b) For r¼ 4
(m Single jet experiments, ~ Twin jet experiments, ——— Single jet CFD
simulations, ??? Twin jet CFD simulations).
5.2.6. Prediction of temperature fluctuation intensity
Figs. 20–22 illustrate the Trms distribution and comparison for
single jet and 2d, 4d, 6d spacing twin jet case for r ¼2,4. Trms is
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
1
0.8
0.6
Y / Rm
0.4
0.2
0
-0.2 0
0.1
0.2
0.3
0.4
8d
-0.4
y
x
-0.6
d
-0.8
6d
-1
TrmsNormalized
1
1
0.8
0.6
0.6
0.4
0.4
0.2
0.2
0
-0.2 0
0.1
0.2
0.3
0.4
5.5d
-0.4
Y / Rm
Y / Rm
0.8
0
-0.2
0
0.1
0.2
0.3
8d
-0.4
y
y
x
-0.6
x
-0.6
d
-0.8
-0.8
4d
-1
0.4
d
6d
-1
TrmsNormalized
TrmsNormalized
Fig. 21. Temperature fluctuation intensity distribution for 4d spacing twin jet on
line 3 (5.5d). (a) For r ¼2. Legend same as Fig. 20(a). (b) For r¼ 4. Legend same as
Fig. 20(b).
Fig. 22. Temperature fluctuation intensity distribution for 6d spacing twin jet on line
4 (8d). (a) For r¼2. Legend same as Fig. 20(a). (b) For r¼ 4. Legend same as Fig. 20(b).
normalized by dividing it with temperature difference between
jet fluid and main pipe fluid.
6. Conclusions
TrmsNormalized ¼
Trms
ðTh Tc Þ
ð10Þ
Fig. 20 shows temperature fluctuation intensity distribution
for 2d spacing twin jet. Temperature fluctuations are higher in the
mixing region of jet fluid and main pipe fluid. For velocity ratio 2,
jet penetrates in the main pipe fluid and peak Trms is attained
below main pipe axis as seen in Fig. 20(a). For higher velocity
ratio of 4, peak Trms value is at the main pipe axis due to greater
penetration of jet in the main pipe fluid as seen in Fig. 20(b). In
both the cases peak for 2d twin jet case is at higher position than
single jet due to higher second jet penetration in cross flow.
As shown previously, the shielding effect of first jet decreases
with increase in jet spacing. For 4d spacing case, the mixing of hot
fluid from first jet causes increase in cross flow temperature. So
the cross flow encountering with 2nd jet is at higher temperature
as compared to single jet case. The local temperature fluctuations
decreases due to reduction in temperature gradient between cross
flow and 2nd jet. Due to this, peak temperature fluctuation intensity
for twin jet case is less than single jet case as seen in Figs. 21(a) and
(b). For 6d spacing case, same trend can be observed from Fig. 22(a).
For higher velocity ratio of r¼4, shielding effect diminishes and the
temperature fluctuations decreases as seen in Fig. 22(b)).
Cross flow thermal mixing experiments were performed to investigate thermal mixing phenomenon in tandem twin jet systems.
Fluid temperature and velocity measurements were carried out
using Hot Film Anemometer modules, CCA and CTA respectively.
Also three dimensional steady state CFD simulations were carried
out to predict velocity and temperature field. Temperature fluctuation intensity was predicted using steady state CFD simulations by
solving transport equation of temperature variance. The predicted
mean velocities and temperatures are in good agreement with the
measurements.
The effect of jet spacing for different velocity ratios is studied
by comparison with single jet case. For 2d spacing case, the first
jet gets pulled by second jet in the downstream for higher velocity
ratio of 4. Also, shielding effect of first jet on second jet results
into higher penetration of second jet in cross flow. The X-velocity
and mean temperature predictions, jet trajectory analysis, centerline velocity decay and vorticity clearly show the interaction
between two jets. For jet spacing more than 4d, there is reduction
in interaction between two jets. For higher velocity ratio and jet
spacing of 6d, the interaction between two jets vanishes.
The results obtained in the present work (both experimental
and CFD simulations) enables calculation of jet spacing required
between two adjacent jets in multiple jet systems issuing to a
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V.S. Naik-Nimbalkar et al. / Chemical Engineering Science 66 (2011) 2616–2626
cross flow. Study of temperature fluctuations occurred due to
thermal mixing is useful in the case of design of mixing elements
of the static mixers and burners in the combustion unit which had
rows of multiple jets entering in the cross flow fluid.
Nomenclature
constant, 0.13
pecific heat of the fluid, J/kg K
branch pipe diameter, m
main pipe diameter, m
jet spacing, m
turbulent kinetic energy, m2/s2
molecular Prandtl number
turbulent Prandtl number
velocity ratio of branch pipe fluid velocity to main pipe
fluid velocity
R
ratio of scalar fluctuation time scale to velocity fluctuation time scale ¼ eT 02 =eT 0 k
radius of main pipe, m
Rm
T
instantaneous temperature, K
T , Tm
mean temperature, K
Trms
root mean square of temperature fluctuations, K
TmNormalized normalized mean temperature
TrmsNormalized normalized r.m.s. temperature
T 02
temperature variance, K2
Tc
main pipe fluid temperature, K
Th
branch pipe fluid temperature, K
instantaneous velocity, m/s
ui
ui
time averaged mean velocity component, m/s
u0i T 0
turbulent temperature fluxes
u0i u0j
Reynolds stresses m2/s2
Vc
main pipe fluid velocity, m/s
CTT
cp
d
D
J
k
Pr
Prt
r
Vh
Vhmax
branch pipe fluid velocity, m/s
maximum branch pipe fluid velocity, m/s
Greek symbol
e
eT 0
r
u
a
aT
m
turbulent kinetic energy dissipation rate, m2/s3
dissipation rate of temperature variance, K2/s
fluid density, kg/m3
kinematic viscocity, m2/s
molecular diffusivity of heat, m2/s
turbulent diffusivity of heat, m2/s
molecular viscosity, kg/m s
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