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SENSITIVITY ANALYSIS TO FLOW SEPERATION OVER NACA4412 AEROFOIL USING RANS SIMULATIONS.
Krishna Zore1 ANSYS, Inc
Pune, Maharashtra, India
Ishan Verma2
ANSYS, Inc Pune, Maharashtra, India
Patrick Sharkey3
ANSYS, Inc Milton Park Oxfordshire, United
Kingdom
ABSTRACT This paper discusses the influence of mesh topology,
turbulence models and various solver numeric settings on
prediction of separated flows over standard NACA4412 aerofoil
at critical angle of attack using ANSYS Fluent flow solver. To
understand the impact of mesh topology the results are compared
between block structured Hex mesh generated in ANSYS
ICEMCFD with prism-tetrahedral and prism-hexcore mesh from
ANSYS Fluent meshing. k-ω based turbulence closure variants
like SST (with default and modified value of a1 coefficient) and
BSL are studied for adverse pressure gradient predictions.
Solution initializations technique, governing equations
discretization methods (first and second order), Under
Relaxation Factors (URFs) and Algebraic Multigrid (AMG)
settings are studied for solver convergence, speed and accuracy.
Computational results were validated against experimentally
available data in the form of aerodynamic forces, pressure
coefficient and velocity profiles. Also, the influence of cross
flow (yaw angle) on the side of body separation were studied by
modeling NACA4412 airfoil, attaching two side plates across
each end. The solver numeric settings, URFs controls and time
advancement (Courant-Friedrichs-Lewy (CFL) and pseudo
transient) methods were explored to better understand side of
body separation bubble prediction.
INTRODUCTION NACA4412 aerofoil is selected for this study due to its
popularity among various applications and easy availability of
geometric profiles and experimental data. The hot-wire
measurement data in the boundary layer and separated region
near wake, acquired for flow past an NACA4412 aerofoil at
maximum lift by Coles & Wadcock5 are used for comparisons.
Figure 1. Shows the development and movement of trailing edge
separation region with increase in angle of attack. For lower
angle of attack less than 50 flow remains fully attached with very
weak link between viscous and in-viscous interactions. For
higher angle of attacks between 50 to 160 the adverse pressure
gradients becomes stronger, which moves separation point
upward and alter flow pattern significantly, making stronger
viscous and in-viscous interactions. After, 160 angle of attack
separations point moves upward more than half of chord length
and destroy suction peak, increasing wake resulting into stall. At
200 angle of attack, flow is completed separated and forms large
turbulent wake resulting into reduction of lift and increase in
pressure drag. Robust solution settings are available for attached
flows but for modeling separated flows needs more
investigation1-3. Mesh resolution, turbulence models and solver
numeric settings plays vital role in accurate predictions for
separated flows.
Figure 1. NACA4412 flow separation phenomenon w.r.t angle of
attack.
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In this paper, the mesh sensitivity study is performed to
understand its impact on the numerical predictions of separated
flows. Block-structured hexahedral meshes are most preferable,
with most RANS turbulence models calibrated on these
structured meshes. However, practical engineering geometries
are very complex and sometimes it’s tedious to generate
structured grids on these geometries. In ANSYS Fluent mesher,
it is now possible to generate hybrid mesh, with surface triangles
to capture the complex geometric features, then extrude prism
wedge cells from the surface, and fill the empty volume with
hexahedral cells, which can leverage some of the benefits of pure
hexahedral mesh. Also, hybrid prism plus tetrahedron meshes are
generated. Results from these unstructured grids (prism hexcore
and prism tetrahedral) are compared to understand the mesh
topology impact. Solution initialization, URFs and advanced
AMG settings are also explored to understand the impact on
solution convergence. Faster convergence leads to reduced
solver iteration requirement, thereby reducing computational
cost. These understandings from flow over an aerofoil led to
generation of best practices for modeling separation due to
adverse pressure gradients. A more complex body separation
phenomenon is also studied which features cross flow (yaw
angle) boundary conditions over NACA 4412 aerofoil with two
side plates attached at the ends. This allows to model complex
flow structures generated due to separation from adverse
pressure gradients, cross flow boundary conditions and side
plates. Finally, the results are compared to the experimental data
in the form of aerodynamic force coefficient (lift and drag),
pressure coefficients and velocity profiles.
NOMENCLATURE
k = Turbulent kinetic energy.
ε = Dissipation rate. SST = Shear Stress Transport.
ω = Specific rate of dissipation.
M = Mach number.
α = Angle of attack.
U = Velocity.
𝜌 = Density.
𝜇 = Molecular viscosity.
T = Temperature.
P = Pressure.
𝛾 = Gas constant.
RESULTS AND DISCUSSION This section is divided into multiple sub-sections based on
the sensitivity studies performed.
Mesh Sensitivity Study
Adverse Pressure Gradient Separation Prediction
The mesh topologies are as showed in Figure 2. Where
Figure 2 (a) depicts the prism-tetrahedral mesh and Figure 2 (b)
depicts the prism-hexcore mesh with similar prism cells from the
airfoil surface. Computations are performed at 150 angles of
attack and lift force coefficient is compared between different
grid types.
(a) (b)
Figure 2. NACA4412, Computational domain a) Prism-tetrahedral
mesh and b) Prism-hexahedral mesh.
Figure 3 shows separation due to adverse pressure gradient at 150
angles of attack for a) Prism-tetrahedral mesh and b) Prism-
hexcore mesh. Figure 4. shows the prediction of adverse pressure
gradient separation on the upper surface of NACA4412 aerofoil,
using SST turbulence model at 150 angles of attack. Figure 4 (a)
and (b) represents the separation region modeled by prism-
tetrahedral and prism-hexahedral mesh respectively.
(a)
(b)
Figure 3. NACA4412, α=150, Separation Prediction a) Prism-
tetrahedral mesh and b) Prism-hexcore mesh.
It is clearly seen, that onset prediction of separation by prism-
tetrahedral mesh is not smooth and infer certain waviness,
whereas the onset separation prediction by prism-hexahedral
mesh is smooth. The reason being the shape of tetrahedral cells,
which are not properly align with the flow direction and might
have some influence on the gradient calculations. Whereas
hexahedral cells remain properly align with the flow directions
and might have very little influence on the gradient calculations.
However, the most important thing is both the meshes predict
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onset separation at same location and this is due to same surface
triangular mesh and the same number of prism cells.
Figure 4. NACA4412, α=150, Lift force convergence, Prism-tetrahedral
and Prism-hexahedral mesh.
Turbulence Model First and Second Order Discretization
Flow separation prediction from SST k-w turbulence model with
first and second order upwind discretization using tetrahedron
and hexcore meshes is shown in Figure 5 and 6. The first order
upwind discretization fails to capture adverse pressure gradient
separation accurately with tetrahedron mesh, whereas hexcore
grid predicts accurately. However, both the meshes shows
accurate separation prediction with second order upwind
discretization methods.
(a)
(b)
Figure 5. NACA4412, α=150, Separation Prediction, Prism-tetrahedral
mesh a) First order turbulence discretization and b) Second order
turbulence discretization.
Figure 7 and 8 shows the lift force coefficient comparison
between first and second order upwind discretization of SST
turbulence model with tetrahedron and hexahedron mesh
respectively.
(a)
(b)
Figure 6. NACA4412, α=150, Separation Prediction, Prism-hexcore
mesh a) First order turbulence discretization and b) Second order
turbulence discretization.
Figure 7. NACA4412, α=150, Prism-tetrahedral mesh, Lift force
convergence, First and Second Order Turbulence Discretization.
For tetrahedral mesh separation region predicted by first order
discretization method shows unsteady behavior with large
separation region moving over upper surface, resulting in
oscillation of lift coefficient curve, whereas, second order
discretization predict steady separation, resulting in constant lift
coefficient curve, as seen in Figure 7. For hexcore mesh, first and
second order discretization produce steady separation, resulting
into constant lift coefficient curve with second order predicting
higher lift coefficient value as shown in Figure 8.
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Figure 8. NACA4412, α=150, Prism-hexcore mesh, Lift force
convergence, First and Second Order Turbulence Discretization.
Total height of prism padding.
Figure 9 (a) and (b). shows the hexcore mesh with prism padding
total height of 5mm and 26mm respectively. The first layer
height and the growth rates are similar between the paddings.
Reason for this study is to access the impact of total prism
padding height on the separation prediction and the integral force
coefficient. Since to have thicker prism padding more numbers
of prism layers needs to be added, which increases the total
number of cell count.
(a) (b) Figure 9. NACA4412, α=150, Prism-hexahedral mesh, (a) 5mm total
prism height (b) 26mm total prism height.
Figure 10 (a) & (b). shows the comparison of adverse pressure
gradient separation region predicted by 5mm and 26mm prism
total height using SST turbulence model. It is observed that both
the meshes predict similar separation regions. However, looking
at Figure 11. the lift coefficient predicted by 5mm prism total
height is slightly higher than 26mm prism total height. Which
indicates 26mm total height predicts slightly more separation.
Since the difference is not huge user can take a call based on his
experience what prism total height is best.
Solution Convergence and Speed Sensitivity Study
Solution Initialization Sensitivity
To understand impact of solution initialization on flow
separation, angle of attack used is 180 at which NACA 4412
configuration stalls. Three different strategies have been used
which are assessed based on faster convergence. Figure. 12
shows convergence behavior of lift coefficient using Hexcore
mesh with 2nd order turbulence discretization. Standard
initialization (red) computes domain values based on inlet
boundary specification. Hybrid initialization (green) solves for
20 iterations of methods which are recipes and boundary
interpolation methods. Velocity field is calculated with Laplace
equation using velocity potential, with velocity components
obtained from gradient of velocity potential. Most efficient way
of initializing external aero flows is by using Full Multigrid
Initialization (FMG) which provides appropriate solution at
minimum cost (blue). It can be seen from Figure. 12 that FMG
initialized solution converges faster and is more robust for flows
with separation.
(a)
(b)
Figure 10. NACA4412, α=150, Separation region, Prism-hexahedral
mesh (a) 5mm total prism height (b) 26mm total prism height.
Figure 11. NACA4412, α=150, Prism-hexahedral mesh, lift coefficient
5mm and 26mm total prism height.
Figure 32. Convergence trace of RANS solution of lift coefficient with
a) standard (red), b) hybrid (green) and c) FMG (blue) initialization.
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Advance Algebraic Multi-grid (AMG) sensitivity
Algebraic Multigrid (AMG) schemes are popular for
efficient usage with unstructured grids, with solution from coarse
level equations without use of geometry or re-discretization.
Scalar system of equations is solved by using Gauss-Seidel or
Incomplete Lower upper (ILU) point smoother methods, while
coupled system of equations are solved with block-method
(Gauss-Seidel or ILU) smoothers. Pressure Based Coupled
Solver (PBCS) Baseline AMG settings are very conservative
which are based on internal knowledge. These settings provide
deeper convergence while supporting different grid types.
Baseline settings use ILU for both point and block method
smoothers. Optimised AMG settings in this study are termed ad
Modified AMG settings which use Gauss-seidel for point-
method smoother and ILU for block-method smoother. Table 1
shows comparison between solver time for convergence of lift
coefficient for PBCS AMG settings (Default and New) and
Pseudo transient methods.
Table 1. Impact of AMG settings on convergence.
Modified AMG settings for flow over aerofoil at α=150 provide
faster convergence for solution with improvement in run time by
35%. Figure. 13 shows that both PBCS settings predict lift
coefficient with less sensitivity, but time taken per iteration is
less for case-specific modifications to scalar and coupled system
of AMG solver.
Figure 14. Convergence of lift coefficient with x-axis representing solver
time per iteration.
CFL and URF relaxation sensitivity
Convergence of PBCS solution largely depends upon CFL
number used. In this section two approaches have been used- a)
3-step approach, CFL 50 with pressure and momentum relaxed
to 0.25 for 1st 30 iterations followed by CFL 200 with pressure
and momentum relaxed to 0.5 for 120 iterations and rest
simulation with CFL 100; b) 2-step approach, CFL 100 with
pressure and momentum relaxed to 0.4 for 200 iterations
followed by CFL 200 for complete solution. Other two
approaches used in this study are a) 2-step approach with fast
AMG, where above mentioned less conservative AMG settings
are used with FMG initialization and b) 2-step approach with
turbulence URF are relaxed to 0.8 for 1st 200 iterations followed
by URF of 0.95.
It can be seen from Figure. 14 that 2-step and 3-step approaches
produce similar convergence behavior. However, 3-step
approach is preferred for case where larger sensitivity to flow
separation is encountered. For most cases 2-step approach is
robust since minimum CFL is >= 100. FAST AMG settings
converge slightly early however as discussed earlier cpu-time of
fast AMG setting is 34% faster. The main impact on cpu-time to
convergence is of relaxation of turbulence quantities. With
relaxation solver takes more number of iterations and more cpu-
time to converge the problem.
Figure 15. convergence of lift coefficient with different CFL and URF
settings.
Complex Cross Flow (yaw angle) Investigations
To investigate the prediction of side of body separations due to
cross flow (yaw angle), two end plates are attached to the
NACA4412 aerofoil with finite span, Figure 15. The
computational domain with boundary conditions are shown in
Figure 16. The mesh resolution with prism-hexahedral and pure
hexa block mesh are shown in Figure 17.
The results are obtained with SST turbulence model at α = 200
and β = 60 with prism-hexahedral and pure hexa block mesh. It
is observed that the turbulence URFs values plays very important
role in predicting side of body corner flow separations. Figure 18
shows lift coefficient curve comparison with two different URFs
values on prism-hexahedral mesh, where lower value of URFs
predict lower lift coefficients. The reason being the over
prediction of separation region with smaller values of URFs
compared to the larger values, Figure 19. Similar impact of
URFs is also observed with pure hexa block mesh. However, the
averaged integrated lift coefficient values are closed (Figure 18),
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the side of body separation predicted with lower URFs is higher.
The reason is for such a complex flow with corner plates under
relaxing the solution with lower URFs values locks the solution
at different levels and does not come out of it. Thus, it is very
important, to increase the URFs to ~1 while modeling such
complex flow physics. Pseudo transient results and more details
will be present in final paper.
Figure 15. NACA4412 aerofoil, with end plates on either side.
Figure 16. NACA4412 aerofoil, computational domain with boundary
conditions to modeled cross flow.
(a) (b) Figure 17. NACA4412 aerofoil mesh resolution (a) prism-hexahedral
(b) pure block hexa.
Figure 18. NACA4412, α=150, 𝛽 = 60, lift coefficient, prism-
hexahedral mesh.
(a) (b) Figure 18. NACA4412, α=150, 𝛽 = 60, lift coefficient, prism-
hexahedral mesh (a) turbulence urfs 0.8 and (b) turbulence urfs 0.95.
Figure 19. NACA4412, α=150, 𝛽 = 60, lift coefficient, pure hexa block
mesh.
(a) (b) Figure 20. NACA4412, α=150, 𝛽 = 60, lift coefficient, pure hexa block
mesh (a) turbulence urfs 0.8 and (b) turbulence urfs 0.95.
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A section including results comparison with experimental data
will be covered in the final paper.
Acknowledgments
The authors would like to thank Domenico Caridi, Matteo
Aroni and Florian Menter from ANSYS for reviewing the results
and providing valuable suggestions.
REFERENCES 1. Wu, J. C., Sampath, S., and Sankar, N. L., “Dynamic
tall of and Oscillating Airfoil,” Proceedings of AGARD
conference on Un-steady Aerodynamics, NATO,
advisory Group of Aero. Research & Development,
977, pp. 24-1 to 24-18.
2. Steger, J. L., ‘'Implicit Finite Difference Simulation
of Flow About Arbitrary Two-dimensional
Geometries,” AIAA Journal, Vol. 16, July 978, pp.
679-686.
3. Gibeling, H. J., Shamroth, S. J., and Eiseman, P. R.,
"Analysis of Strong Interaction Dynamic Stall for
Laminar Flow of Airfoils, "NASA CR-2969, 1978.
4. Donald Coles and Alan J. Wadcock. "Flying-Hot-wire
Study of Flow Past an NACA 4412 Airfoil at Maximum
Lift", AIAA Journal, Vol. 17, No. 4 (1979), pp. 321-
329.
5. Menter, F. R., “Influence of Freestream Values on the
6. K-w Turbulence Model Predictions,” AIAA Journal ,
Vol. 30, No. 6, 1992, pp. 1651–1659.
7. Menter, F. R., “Two-Equation Eddy-Viscosity
Turbulence Models for Engineering Applications,”
AIAA Journal , Vol. 32, No. 8, 1994, pp. 1598 – 1605.