JOURNAL OF AIRCRAFT
Vol. 32, No. 1, January-February 1995
Study of the Droplet Spray Characteristics of a Subsonic
Wind Tunnel
Michael B. Bragg* and Abdollah Khodadoustt
University of Illinois at Urbana-Champaign, Urbana, Illinois 61801
A finite difference, two-dimensional potential flow solver, and a three-dimensional particle trajectory code
have been written to compute water droplet trajectories in a subsonic incompressible flow wind tunnel. This
method was used to study the spray cloud in the test section of a two-dimensional wind tunnel resulting from
the injection of a distribution of water droplets in the settling chamber ahead of the inlet. The results of this
computational study showed that the trajectories of the larger water droplets were affected by the droplet inertia
and gravity more dramatically than that for the smaller particles. The calculated liquid water content across
the test section indicated a high concentration near the tunnel centerline. The largest droplets were present at
the test section only in the center one-third of the wind tunnel, whereas the smaller droplets spanned almost
the entire test section width. This resulted in a computed droplet size distribution skewed toward the larger
droplets in comparison with the initial Langmuir-D distribution. The distribution of particle sizes and concen-
trations required at the droplet injection point in the settling chamber for a Langmuir-D distribution of uniform
liquid water content in the center third of the test section was computed.
A
CD
CR
Fr
8
H
Hs
K
S
t
u
u
v
P
a
T
0)
Nomenclature
droplet trajectory stream tube area
droplet drag coefficient
tunnel contraction ratio, Hf/HTS
Froude number, £/TS/V//,-g
gravitational acceleration constant
tunnel width
flowfield total head, Ptotal/p
droplet inertia parameter,
z =
Subscripts
TS
= droplet freestream Reynolds number,
stream function
time
average flow speed at an x location
local flow speed in x direction
local flow speed in y direction
tunnel Cartesian coordinate system
droplet diameter
droplet nondimensional position
air density
droplet density
nondimensional time, Ut/H,
flow vorticity
= tunnel inlet value
= tunnel test section value
Superscripts
= vector quantity
= first derivative with respect to r
= second derivative with respect to T
Received Feb. 23, 1994; revision received May 28, 1994; accepted
for publication May 30, 1994. Copyright © 1994 by M. B. Bragg and
A. Khodadoust. Published by the American Institute of Aeronautics
and Astronautics, Inc., with permission.
*Associate Professor, Department of Aeronautical and Astro-
nautical Engineering. Associate Fellow AIAA.
tPostdoctoral Research Associate, Department of Aeronautical
and Astronautical Engineering. Student Member AIAA.
Introduction
D URING flight in adverse weather conditions, an aircraftis subjected to water droplet impingement. Given the
proper conditions, the impinging water may freeze on the
flight surfaces, reducing their aerodynamic efficiency. To pro-
vide the aircraft all-weather capability, anti-icing and de-icing
systems are used on the leading edge of the most flight-critical
surfaces. In order to determine the extent of the surface that
is to be protected by the anti- or de-icing equipment, and the
amount of protection needed, it is necessary to know the
details of the water droplet impingement on the surface.
Computational methods have been developed to calculate
water droplet impingement on airfoils and wings. 1 ~ 6 Wind-
tunnel tests have been conducted in icing tunnels to measure
impingement characteristics for code validation.7"9 While the
existing codes calculate the impingement efficiency in free air,
the validation studies are performed in wind tunnels where
the tunnel walls can affect the droplet trajectories. The wall
effects have been found to be small and within the limits of
experimental error for most two-dimensional airfoil testing in
a typical subsonic wind-tunnel test section, without accounting
for the upstream inlet contraction effects on the water droplet
trajectories.10 Effects of the wind-tunnel walls on the com-
puted trajectories in a three-dimensional flowfield with a re-
flection-plane mounted rectangular wing are currently under
investigation.11 These early three-dimensional results show
trends similar to the two-dimensional wall effects.
The previous wall-effects studies10-11 assumed that the wind-
tunnel spray system had been adjusted to provide a uniform
cloud in the test section with regards to both droplet size and
liquid water content. These studies then examined the effect
of the wind-tunnel walls on the aerodynamics of the airfoil
or wing and how this affected its droplet impingement char-
acteristics. This study is intended to provide insight into how
the wind-tunnel contraction affects the water droplet cloud
in the test section, and how the initial spray cloud can be
modified to provide a uniform test section cloud.
Numerical Formulation
Flowfield
The flowfield solution technique employed here was used
by Coirier12-13 to study the effect of screens on two-dimen-
sional inlets using a finite difference method for subsonic
199
200 BRAGG AND KHODADOUST: DROPLET SPRAY CHARACTERISTICS
201 x51 grid
x/H.
Fig. 1 Computational grid in the physical domain.
inviscid incompressible flow. The stream function S satisfying
the continuity equation is defined such that the velocity field
is given by
dS dS
' dx (1)
Substitution into the momentum equation leads to the fol-
lowing Poisson equation:
(2)
where 3Hs/dS is defined as the source term P(S). Introducing
a Laplace equation of a different variable TV as
Nxx + NVY = 0 (3)
and inverting the Poisson system of Eqs. (2) and (3) yields
the following elliptic partial differential equations that are
solved in the rectangular computational domain:
AXSS - 2BXsn + CXnn = -J2(PXS) (4)
AYSS - 2BYsn + CYnn = -J2(PYS) (5)
A = XI + Yl (6)
B = YsYn
C = X* + Y2S
J = XsYn - XnYs
(7)
(8)
(9)
These equations determine the X and Y locations of the
constant S (streamlines) and constant N lines in the physical
domain. The transformation yields the flow streamlines, thus,
the generation of the elliptic grid yields the velocity field using
Eq. (1). Figure 1 shows the computational grid in the physical
domain with the inflow and outflow planes set one inlet length
upstream and downstream of the inlet and exit planes, re-
spectively. This boundary placement will allow the flow angle
distribution to smoothly approach zero at the inflow and out-
flow planes.
Equations (4) and (5) were solved using second-order cen-
tral and one-sided finite differences in a successive line-re-
laxation method. The value of the S on the upper and lower
boundaries and the flow angle at the inflow and outflow planes
served as the boundary conditions on the rectangular com-
putational domain. The value of the total head gradient or
P(S) was set to zero for this study, except for the special case
described in the Code Verification section.
Particle Trajectory
Assuming a low concentration of spherical droplets of con-
stant mass, Newton's second law of motion in nondimensional
form yields2 14
CDR
24 Fr2.
where the droplet Reynolds number is
R = (11)
The velocity u/U in Eqs. (10) and (11) are determined by
interpolation of velocities obtained from the finite difference
solution of the flowfield. The particle drag is calculated by
the method of Langmuir and Blodgett,15 which yields the
following form in the trajectory equation above:
24 = 1.0 + 0.197/?
(1 2.6 x 10"4/?1 (12)
Given the droplet initial conditions in addition to the free-
stream and droplet size data, the trajectory equation is nu-
merically solved by a predictor-corrector scheme due to Gear.16
In two dimensions, the droplet stream tube areas A,- and
AIS at the inlet and test section, respectively, are obtained
from adjacent droplet trajectories. Then, through the prin-
ciple of mass conservation
LWC,, = LWC, - - (13)
relates the liquid water content (LWC) in the wind-tunnel
inlet LWC,, and test section LWCIS, where droplet evapo-
ration is ignored. The droplet velocity at the inlet plane and
the test section plane are assumed equal to the corresponding
x components of the tunnel velocity. Assuming uniform flow
at the inlet and test section planes, the velocity ratio is 17,7
(7TS, and is equal to the wind-tunnel contraction ratio CR.
Code Verification
The verification of the code was carried out in two steps.
First, the flowfield calculations were verified, and in the sec-
ond step, trajectory computations were verified. An initial
check was performed using a 161 by 31 grid to ensure that
mass was conserved within the tunnel. In an incompressible
flow, the increased velocity in the test section is proportional
to the contraction ratio of the tunnel inlet. The average u
component of velocity, nondimensional with respect to the
test section velocity, should be l/CR at the wind-tunnel inlet.
The average velocities at the inflow plane were within 0.047% ,
proving that mass within the wind tunnel was indeed being
conserved.
A second test of the flowfield was also performed. For an
arbitrary two-dimensional contraction with constant vorticity
everywhere in the flowfield, the analytical solution for the u-
velocity profile may be obtained at the inflow plane by12
M, = -< + (o)Hf/2) + (l/CR)
and at the outflow plane by
u2 = -, fjim
6.31
10.58
14.46
20.36
27.89
35.42
45.19
Mass %
5
10
20
30
20
10
5
droplet diameter = 10.58 microns
Fig. 4 Droplet trajectories for the 10.58-/nm droplet.
0.5
0.4
0.3
0.2
0.1
0.0
droplet diameter = 45.19 microns
Fig. 5 Droplet trajectories for the 45.19-/*m droplet.
velocity was set equal to the tunnel velocity at the injection
point. Droplet trajectories were terminated when the test
section location xlH, = 2.5 was reached.
Figure 4 shows the computed trajectories for the 10.58-/mi
droplets. These droplets follow the flowfield streamlines more
closely than the larger droplets whose trajectories are shown
in Fig. 5. Due to the larger droplet size and mass, the droplets
do not negotiate the turn in the tunnel contraction just prior
to the test section. The droplets' inertia carry them near the
tunnel centerline downstream of the contraction. The larger
droplets have more inertia, and as a result, their ability to
follow the flowfield in regions of high-velocity gradients were
reduced in comparison with smaller droplets.
Since the droplets have size and mass, it is anticipated that
their motion will be affected by gravity. Droplet fallout, de-
fined as the 2 distance traveled by the droplet, is shown in
Fig. 6. The 10.58- and 45.19-jiun droplets were released at
the same x and z, but at different y locations. The droplets
released at y/H,- = 0.40 take more time to reach the test
section than the droplets released at y/Hi = 0.05. Conse-
quently, the fallout for the droplet trajectories originating at
y/H,- = 0.40 was larger. The maximum fallout is computed to
be 0.165 in. for the 45.19-jnm droplet over the 8 ft distance
202 BRAGG AND KHODADOUST: DROPLET SPRAY CHARACTERISTICS
0.0000
-0.0005
-0.0010
-0.0015
-0.0020
-0.0025
-0.0030
8=10.58 Jim
y0=0.05
——— - y0=0.40
8=45.19 M-m
2
x/Hj
Fig. 6 Comparison of the computed fallout for the 10.58- and 45.19-
fjLm droplets.
-•— 8=6.3 ln-m
o 8=10.58fim
- •- S=14.45|im
- - - & - - 8=20.36|im
-^- 6=27.89nm
- — * - • • • 5=35.42^im
V*
0.0 0.1 0.2 0.3
y/HTS
0.4 0.5
Fig. 7 LWCs across the tunnel test section for monodisperse sprays
with the inlet LWC = 1.
from the nozzle location in the inlet to the test section. The
maximum fallout for the smaller droplet is computed to be
0.0133 in. Neither of these fallout distances is considered
significant, particularly since fallout for this two-dimensional
tunnel is in the direction perpendicular to the plane of the
contraction.
In order to investigate the mass distribution across the test
section, the LWC in the test section must be estimated. The
trajectories for seven droplet sizes based on the Langmuir-D
distribution were computed. The LWC in the test section for
the seven droplet sizes are shown in Fig. 7. The distributions
shown are not weighted by the Langmuir-D distribution. They
show the LWC for each droplet size as if a separate mono-
disperse cloud was tested at each droplet size. The results
reflect the trend seen in the individual particle trajectories
shown in Figs. 4 and 5. The smaller droplets are able to follow
the flowfield closely and, therefore, their LWC across the test
section is nearly uniform. The smallest droplet at a diameter
of 6.31 fjim has a LWC near 1 at the centerline increasing
slightly as the tunnel wall is approached. The LWC goes to
zero beyond approximately y/Hls = 0.43, where even this
small droplet cannot follow the flow due to the high gradients
in the vicinity of the rapid contraction coming into the test
section. As the droplet size is increased (Fig. 7), the LWC at
the centerline increases and the reduction in LWC to zero
occurs closer to the tunnel centerline. This is of course due
to the increasing inertia of the droplets. For the largest droplet
tested at 45.19 jam, the LWC predicted was 2.27 at the cen-
terline with a rapid increase to 4.73 before dropping to zero
aty/Hls = 0.172.
Test Section Cloud Resulting from a Uniform Inlet Cloud
Now consider a uniform initial cloud at the nozzle plane
that has a Langmuir-D distribution and LWC = 1. Table 1
gives the droplet sizes for a Langmuir-D distribution for a
MVD = 20.36 /xm and the corresponding percentage of the
total mass represented by each droplet. If the tunnel walls
had no effect on the droplet trajectories, a Langmuir-D dis-
tribution with LWC = 1 would be expected across the entire
test section. However, due to the tunnel wall effects in the
inlet, the LWC and droplet size distribution will vary across
the test section. The effect of the tunnel walls on the total
LWC across the test section is plotted in Fig. 8. The curve is
not as smooth as might be expected since only seven droplets
were chosen to represent the distribution, as is typically done
in icing calculations. The LWC is greater than one in the
center of the tunnel due to the increased concentration of
large droplets, and is fairly constant at a LWC ~ 1.35 until
y/H-Ys ~ 0.20. From this location out towards the tunnel wall
the LWC drops rapidly due to the absence of the larger drop-
lets. An LWC = 1.0 is reached at approximately y/HTS =
0.30, and no mass is predicted in the tunnel beyond y/Hls =
0.430.
In an experimental study measuring ice accretion or droplet
impingement, the test section LWC is measured using a ref-
erence collector or other device. During the facility calibra-
tion, the placement of the nozzles in the inlet is adjusted to
provide uniform LWC or ice accretion over as large a portion
of the test section as possible. Thus, a usable cloud of uniform
LWC in the center of the tunnel is available for testing, with
the effect of the tunnel walls on LWC essentially removed.
However, the effect of the tunnel walls on the droplet size
distribution is not so easily measured or corrected.
Figure 9 shows the mass, made nondimensional with respect
to the total mass, for each of the seven droplet sizes at nine
locations across the tunnel test section. Also shown is the
initial Langmuir-D droplet distribution at the inlet from Table
1. The droplet size distributions at the tunnel centerline and
U
1.4
1.2
1.0
0.8
0.6
0.4
0.2
0.0
0
• — • — UIUC 5x1 test section
> ——— -*— ———— ^ -*_^ No wall effect
\\
\
\
\
0 0.1 0.2 0.3 0.4 0.
y/HTS
Fig. 8 LWC across the test section with the inlet LWC = 1 and a
Langmuir-D distribution.
0.7
0.6
0.5
0.4
0.3
0.2
0.1
0.0
-•— Langmuir-D
--o- y/HTS=0
--v-- y/HTS=.06
-•- y/HTS=.12
-B— y/HTS=.18
-*- y/HTS=.24
-*•••• y/HTS=.30
--A- y/HTS=.36
0 10 50 6020 30 40
droplet size (microns)
Fig. 9 Droplet size distributions at several locations across the test
section with the inlet LWC = 1 and a Langmuir-D distribution.
BRAGG AND KHODADOUST: DROPLET SPRAY CHARACTERISTICS 203
a
Q
y/HTS
Fig. 10 Effective MVD across the test section with the inlet LWC =
1 and a Langmuir-D distribution.
the next three stations are very similar. Although shifted to
the right due to the presence of more large droplets than that
found in the Langmuir-D distribution, only a small variation
with tunnel location is seen in this center area of the tunnel.
This region corresponds roughly to the region of constant
LWC in Fig. 8. As would be expected from the results
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