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15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
Impact of a gap on boundary layer transition at Mach 6
Yifei Xue1, Z.J. Wang2, Song Fu1,*
1School of Aerospace Engineering, Tsinghua University, Beijing, China2Department of Aerospace Engineering, University of Kansas, Lawrence, Kansas, USA
*corresponding author: [email protected]
Abstract Laminar-turbulent transition in a hypersonic boundary layer can be influenced by imperfections on the
wall surface. Transition can be delayed or accelerated depending on the type, configuration and location of the
imperfections. Both natural transition and the transition triggered by the imperfections are poorly understood. This
paper studies a Mach 6 transitional flow over a flat plate with a gap, which is a simple geometry of the imperfection.
We investigate the interaction between the gap and forcing waves using a high order implicit large eddy simulation
tool. The forcing waves are obtained by combining a two dimensional instability wave and a pair of sub-harmonic
three dimensional instability waves. First, flow structures including expansion and shock waves near the gap are
analyzed to illustrate the basic flow. Second, we compare the behavior of transition processes of two angles of
attack, AoA = 0◦ and AoA = −7◦. The skin friction coefficient distribution with a gap at AoA = 0◦ is almost thesame as that without a gap, which indicates that the transition process is not disturbed by the gap. In contrast,
a slightly earlier transition is observed with a gap at AoA = −7◦ than without a gap. At AoA = −7◦, a Fourieranalysis shows that new disturbances with broadband frequencies are triggered in the gap, propagate downstream
and influence the amplification of the instability modes.
Keywords: Hypersonic transition, implicit large eddy simulation, gap, high order
1 Introduction
Imperfections or roughness elements may trigger an early transition or late transition in a hypersonic boundary
layer. A two dimensional (2D) gap is one of the simplest geometric imperfections. The influence of a 2D gap
on transition has been well studied under subsonic flow conditions. Many criteria [1] are proposed to predict
the effects of imperfections on transition. A gap is favorable to the substantial downstream TS-growth when
the gap is located after the neutral point. To trigger an early transition, the Reynolds number based on the
characteristic length of the imperfection is always found to be larger than a critical Reynolds number.
In transonic flows, the increase in Mach number can stabilize two and three dimensional modes in an
open-cavity flow according to Sun[2]. However, there are few studies on hypersonic transitional flow due to
imperfections, such as the 2D gap. The free stream turbulence is considered to be composed of slow acoustic
waves, fast acoustic waves, vorticity waves and entropy waves. Two discrete modes originating from the slow
and fast acoustic branches in the eigenvalue spectrum[3], fast discrete mode (mode F) and slow discrete mode
(mode S), are the two major modes in a hypersonic boundary layer. When mode S and mode F have the same
phase velocity, a synchronization occurs. We name the point the synchronization point. The boundary layer
is table before the neutral point (the neutral position of the lower branch of the neutral curve) because the
disturbances are damped outside the neutral curve. An imperfection located before the neutral point does not
trigger an amplification of the disturbance. When the imperfection is located between the neutral point and the
synchronization point, the growth of the disturbance can be accelerated. Mode S can be amplified when a bump
imperfection is placed upstream of the synchronization point[4]. The imperfection has the largest influence
when it is close to the synchronization point[5]. In another study, a 2D imperfection located downstream of
the synchronization point is shown to decrease the Mack second mode[6]. However, only little influence on
instability modes such as mode S[7] can be observed with the analysis of stability theory. Transitional processes
interact with two dimensional imperfections (i.e., oblique wave breakdown or subharmonic wave breakdown)
in a hypersonic boundary also need to be investigated.
Besides the existing instability modes, frequency change[8] or new instabilities can also be triggered by
imperfections. For example, the Kelvin-Helmholtz instability of a shear layer[9]. In addition, two kinds of
oscillation mechanisms[10] within the gap are observed in supersonic transitions. Gap flows in this work can
Paper ID:312 1
15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
be classified open cavity flow which has two oscillation mechanisms[11]. The first one is the longitudinal
oscillation which corresponds to the Rossiter mode[12]. The reflected acoustic wave propagates from the aft
corner to the front corner. The other one is the transverse oscillation. The transverse mechanism has a feedback
loop within the cavity. The reflected acoustic wave firstly propagates down to the bottom of the gap and
then transverses to the shear flow. Phenomenons of longitudinal and transverse mechanisms can be observed in
experiments at Mach 1.71[10]. In a hypersonic flow, these new instability modes need to be further investigated.
The main contributions of this study include: the wall-resolved large eddy simulations (LES) of a Mach 6
hypersonic subharmonic transitional flow over a flat plate with a single 2D gap at two angles of attacks, and
a detailed analysis of the forcing instability waves on the accelerated transition process. The neutral positions
of the forcing waves are analyzed with a linear stability theory. The oscillation mechanisms of two angles of
attack are studied by decomposing the instability waves with a Fourier transformation.
2 Numerical Method
This section briefly reviews the numerical method used in the present study. The high order solver, hpMusic, is
based on the flux reconstruction (FR) or correction procedure via reconstruction (CPR) method. This method is
originally developed by Huynh [13] for hyperbolic conservation laws, and later extended to mixed meshes by
Wang and Gao, and Haga et al[14][15][16]. Other developments in the FR/CPR methods are reviewed in [17].
We choose the FR/CPR method because of its ability in handling unstructured meshes, its high-order accuracy,
its simplicity like a finite difference method, and its scalability on supercomputers. The unsteady compressible
Navier-Stocks equations are discretized using the with FR/CPR method. We use the following conservation
law to introduce the basic idea
∂U
∂ t+∇ ·F(U) = 0, (1)
where U is the vector of conservative variables, and F is the flux vector. The computational domain is dis-
cretized with non-overlapping elements Vi. In each element, the conservation law is transformed into a weighted
residual form with an arbitrary test function W
∫
Vi
(∂U
∂ t+∇ ·F(U))WdV = 0. (2)
The conservative variables U is assumed to be a polynomial of degree k, Ui ∈ Pk. Using integration by parts in
the second term, we arrive at
∫
Vi
∂Ui∂ t
WdV +∫
∂ViWF(Ui) ·ndS−
∫
Vi
∇W ·F(Ui)dV = 0. (3)
We replace the normal flux term at element interfaces with a common Riemann flux Fncom to achieve conserva-
tion. Applying integrating by parts again to∫
Vi∇W ·F(Ui)dV , we obtain
∫
Vi
∂Ui∂ t
WdV +∫
∂ViW [Fncom −F
n(Ui)]dS−∫
Vi
W∇ ·F(Ui)dV = 0. (4)
The Riemann flux Fncom is computed with the Roe Riemann solver by the use of Vi and Vi+, in which the subscript
"i+" denotes the neighbor element
Fncom = Fn
com(Ui,Ui+,n). (5)
In order to simplify (4), we replace the surface integral with a volume integral via a lifting operator, δi ∈ Pk(Vi):
∫
∂ViW [Fncom −F
n(Ui)]dS =∫
Vi
WδidV. (6)
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15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
Fig. 1 Schematic of the computational domain
Substituting (6) into (4), we obtain
∫
Vi
[∂Ui∂ t
+∇ ·F(Ui)+δi]WdV = 0. (7)
The aim of introducing the lifting operator is to derive the differential equation from the integral one. As-
suming that the flux vector F(Ui) can be approximated with a polynomial, then we obtain the final formulation:
∂Ui, j∂ t
+∏ j(∇ ·F(Ui))+δi, j = 0, (8)
where ∏ j denotes a projection to the polynomial space and the subscript j represents the projection at the
solution point j, ∏ j(∇ ·F(Ui)) ∈ Pk.
The FR/CPR method converts the weighted residual form from an integral one to a differential one. It is
compact in that the scheme only needs the immediate face neighbors. The viscous flux in the compressible NS
equations is computed with the Bassi-Rebay 2 (BR2) scheme[18]. No explicit subfilter scale models are used.
Therefore the present approach is called an implicit LES or ILES. The backward-difference formula (BDF2)
with a LU-SGS solver[19] and a 3rd Runge-Kutta method are employed for time marching. An accuracy pre-
serving limiter [20] is adopted to capture shock-waves and maintain the high order accuracy of the simulations
elsewhere. The LES tool has gone through an extensive verification and validation process[21].
3 Simulation results and discussions
3.1 Computational setup
To investigate whether a 2D gap affects the subharmonic transition of a Mach 6 hypersonic flow, we perform a
wall-resolved ILES of the transitional flow. In order to avoid the difficulty of simulating a strong leading edge
shock with a high order method, the computational domain starts behind the leading edge and ends after the
formation of the turbulent boundary layer. The gap configuration and the computational domain are illustrated
in Fig. 1.
A laminar boundary layer profile is prescribed at the inflow boundary. The freestream Mach number is
M∞ = 6 and the free-stream unit Reynolds number is Re∞ = 1.0×107/m, the static temperature is T∞ = 55K.
The inflow conditions are of the same order of magnitude as the parameters of the turbulent wind tunnel at
Peking University. The computational domain is 0.02 ≤ x ≤ 0.7m in the streamwise direction and 0.0 ≤ z ≤0.018m in the spanwise direction. Two complete oblique forcing waves are generated at the disturbance stripin the spanwise direction. The instability waves are introduced to the flow by blowing and suction at the
disturbance strip. The gap starts at x = 0.2m and ends at x = 0.22m with a depth h = 0.01m. A periodicboundary condition is used in the spanwise direction. Buffer region are adopted at both the right end and the
top of the domain.
Next we explain the method of blowing and suction. Simultaneous blowing and suction is used in this work
to make sure no additional fluid is added into the flow. The temperature on the disturbance strip is replaced
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15th International Conference on Fluid Control, Measurements and Visualization
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Fig. 2 Slice of mesh for AoA = 0◦ gap flow
with an isothermal condition[22]. The temperature equals the adiabatic wall temperature of the steady solution.
Following the blowing and suction function of Huai et al[23] , the wall-normal velocity V is prescribed as:
v(x,z, t) = A2D f (x)sin(ω2Dt)+A3Dg(z) f (x)sin(ω3Dt), (9)
where, A2D and ω2D are the two dimensional wave’s amplitude and frequency, respectively. A3D and ω3D are
the oblique wave’s amplitude and frequency. Then the shape function is defined following Fasel et at[24]:
| f (ξ )|= 15.1875ξ 5 −35.4375ξ 4 +20.25ξ 3,
g(z) = cos(2πz/λz).(10)
ξ can be obtained with xm = (x1 + x2)/2:
ξ =
x− x1xm − x1
x1 ≤ x ≤ xm,
x2 − x
x2 − xmxm ≤ x ≤ x2.
(11)
The location of disturbance strip in the streamwise direction is 0.035 ≤ x ≤ 0.055m (x1 = 0.035m and x2 =0.055m). To obtain a subharmonic transition in the computational domain, a two dimensional wave and a pairof subharmonic oblique waves are added in the disturbance strip. Frequencies of the oblique waves are one half
of that of the two dimensional wave. The resonance of the three waves leads to the subharmonic transition[25].
The disturbance amplitude A and dimensionless frequencies F of AoA = 0◦ are set to:
A2D = 2%U∞, F2D = 0.6×10−4;
A3D = 2%U∞, F3D = 0.3×10−4.
(12)
A negative angle of attack leads to adverse pressure gradient which contributes to the transition. So the distur-
bance amplitudes at AoA =−7◦ are set to smaller values:
A2D = 1%U∞, F2D = 0.6×10−4;
A3D = 0.05%U∞, F3D = 0.3×10−4.
(13)
The ω3D and ω2D can be calculated with:
ω =FU2∞
ν. (14)
The mesh used in the simulation ( i.e., a slice mesh of gap flow at z = 0.009m, AoA = 0◦) is illustrated inFig. 2. Mesh in region x ∈ (0.5,0.7)m is progressively coarsened in the streamwise direction which can reducethe disturbances from outflow boundary. The degree of freedoms (DOFs) in each directions are lists in Table 1
where DOFsin and DOFsout denote the DOFs in the gap and out of the gap, respectively.
3.2 Stability analysis of the instability waves
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15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
Table 1 Grid resolution of the simulation
nx ny nz ∆x+max ∆y
+max ∆z
+max
gap DoFsin 70 81 140
DoFsout 1544 94 140 5.7(AoA = 0◦) 2.5(AoA = 0◦) 2.4(AoA = 0◦)
/10.3(AoA =−7◦) /4.7(AoA =−7◦) /4.3(AoA =−7◦)
smooth DoFs 1544 94 140 5.7(AoA = 0◦) 2.5(AoA = 0◦) 2.4(AoA = 0◦)/10.3(AoA =−7◦) /4.7(AoA =−7◦) /4.3(AoA =−7◦)
Before the implicit large eddy simulation, we need to choose a reasonable inflow disturbance for the hyper-
sonic boundary layer. Stability characteristics of disturbance strip are investigated by LST in this part. We can
compare the gap location with the neutral point and the synchronization point through the stability analysis.
The LST analysis explains why we choose the frequencies of two dimensional wave F2D = 0.6×10−4 and
the subharmonic oblique waves F3D = 0.3×10−4 at the disturbance strip. Here we start with the introduction
of LST[26]. The basic flow for the LST analysis is computed from the compressible Blasius boundary layer
equations. The governing equations derived from compressible Navier-Stocks equations can be separated into
the basic-state equations and the disturbance equations. The form of the disturbances are assumed to be:
q̃(x,y,z, t) = q̂(y)exp(i(αx+β z−ωt))+ c.c., (15)
where c.c. stands for complex conjugate. In spatial stability, α = αr + iαi is the complex streamwise wavenum-ber, β is the spanwise wave number and ω is the angular frequency. We denote the Reynolds number based on
boundary layer thickness with R, and then the eigenvalue problem can be expressed as:
α = f (β ,ω,R). (16)
For β = 0, the neutral curve obtained from LST is shown in Fig. 3(a). Instability wave with a frequency ofF2D = 0.6× 10
−4 will grow within the computational domain. The synchronization point of two dimensional
instability wave predicted in Fig. 3(b) is x = 0.3635m. The gap is upstream of the synchronization point.Growth of instability wave F2D = 0.6× 10
−4 should be affected by the gap according to LST analysis. Gap’s
effect on transition process is discussed with ILES results in the next part.
(a) Neutral curve for β = 0
(b) Phase velocity of mode F and mode S
Fig. 3 LST results
Then we fix R = 741.63 (x = 0.055m, end of the disturbance strip), the contour levels of αi can be obtainedwith LST. As shown in Fig. 4, the oblique disturbance (F = 0.3×10−4, β = 0.0405) locates inside the neutralcurve (αi < 0). So the oblique waves will grow in downstream direction.
We can conclude that the current instability waves will grow monotonously. The oblique transition process
with current forcing frequencies and wave numbers is expected to be affected by the gap.
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15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
Fig. 4 Neutral curve for R = 741.63
Fig. 5 Overall vortex evolution of the gap flow transition process, AoA = 0◦
3.3 Transition processes at two angles of attack
Gap flow of AoA = 0◦
Complete transition processes of smooth and gap flows are obtained with ILES. Similarity results of compress-
ible boundary layer equations are imposed at the inflow boundary. Subharmonic transitions are induced by the
forcing instability waves at disturbance strip. An overview of gap flow transition process at AoA = 0◦ demon-strated with vortices is shown in Fig. 5. Vortices are visualized with Q-criterion colored with non-dimensional
streamwise velocity. The background is the numerical schlieren. Forcing disturbances grow in boundary layer
and trigger the transition. Two pairs of λ vortices are obtained in spanwise direction at the transition onset. The
vortex heads grow in normal direction and interact with the boundary layer when approaching the boundary
layer, as shown in Fig 6(a). Multiple hairpin vortices are observed in Fig 6(b). The hairpin vortices are hard
to be distinguished because the interaction between the boundary layer and the hairpin vortices. Complicated
vortices are observed in the later stage of transition, shown in Fig 6(c). Mixture of large and small vortices
leads to the turbulent boundary layer.
(a) First stage (b) Second stage (c) Third stage
Fig. 6 Three vortex stages of the gap flow transition process, AoA = 0◦
The transition process of smooth flat plate is almost the same with that on gap case. The gap has little effect
on the transition process at AoA = 0◦. However, there are some local flow structures occur at the corner of thegap, as shown in Fig. 5. So the flow at the gap is particularly discussed. Averaged pressure and streamlines are
used to illustrate the flow near the gap in Fig. 7. Three separations are observed in the gap including one main
separation and two small separations on each side of the main separation. Velocity in the gap is mostly less than
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15th International Conference on Fluid Control, Measurements and Visualization
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Fig. 7 Averaged pressure distribution and streamwise in the gap at the center z-plane
Fig. 8 Instantaneous slice of streamwise velocity at x-z-plane
1% of the velocity outside the boundary layer which indicates that the gap is nearly a dead zone. The maximum
velocity locates at the upper border of the main separation as a result of the acceleration of the expansion from
the upstream corner. An expansion is followed by a shock at the downstream corner which decelerates the
flow to an undisturbed condition. The expansion and shock are weak that the streamlines at y = 0m are nearlyundisturbed by the gap.
The instantaneous streamwise velocity evolution above the cavity is illustrated in Fig. 8 at the position of
y = 0.0075x+ 0.00105m. A local acceleration is observed at the gap and the streamwise velocity decreaserapidly after the gap. This confirms the velocity acceleration at the gap in the time-averaged results. No special
change on the streamwise velocity is observed far behind the gap comparing with the velocity evolution in
smooth flow.
For the current forcing waves, transition phenomenons of smooth flow and gap flow are the same. The in-
fluence of the gap is limited to the vicinity of the gap based on the time-averaged results and the instantaneous
results. As a result, the distribution of skin friction coefficient of gap flow is nearly same with the smooth one
except for the vicinity of the gap, as shown in Fig. 9.
Gap flow of AoA =−7◦
Hypersonic aircrafts usually have a slender, streamlined fuselage to reduce the drag. In addition, the angle
of attack of the cruise phase is usually limited to several degrees. We choose a possible angle of attack to inves-
tigate how the angle of attack influences the transition process. A negative angle of attack is likely to occur on
Fig. 9 Time-averaged and spanwise-averaged distribution of skin friction coefficient at AoA = 0◦
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15th International Conference on Fluid Control, Measurements and Visualization
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Fig. 10 Instantaneous slice of streamwise velocity at x-z-plane
Fig. 11 Time averaged and spanwise averaged distribution of skin friction coefficient at AoA =−7◦
the aircraft surface which means the fluid flow toward the the surface. Transition processes of AoA =−7◦ gapflow are studied in this part. Numerical results of laminar flat plate are imposed at the inflow boundary, which
are derived from a simulation of a complete geometry including the leading edge. Typical flow structures of the
transition at AoA =−7◦ are nearly the same with AoA = 0◦ case. However, the appearance of the λ vortices isearlier than AoA = 0◦ case. Contour of instantaneous streamwise velocity at the slice of y = 0.005x+ 0.0005illustrated in Fig. 10 shows a higher amplification of three dimensional instability waves after the gap.
Since the larger wave amplification in the AoA = −7◦ gap flow, a relatively earlier transition is observedcomparing to the smooth flow at AoA =−7◦.
3.4 Influence of the angle of attack on the transition process
A gap flow at AoA = 0◦ has almost the same transition process as the corresponding smooth flow. How-ever, when the angle of attack is negative, a gap can trigger an earlier transition compared to the corresponding
smooth one. In order to find out the mechanism of the interaction between forcing instability wave and gap, we
perform Fourier transformations at both angles of attack.
Mode amplitude curves in streamwise direction are plotted in Fig. 12 and Fig. 13. Modes ( f ,k) are denotedby frequency f and spanwise wave number k, where f = 1 denotes the forcing frequencies of the oblique waves(F = 0.3×10−4) and k = 1 denotes the fundamental wave number in spanwise direction (two complete waves).For each mode, Y-axis denotes the maximum streamwise velocity perturbation in boundary layer, which is
non-dimensionalized with the freestream velocity.
Modes in the gap flow at AoA = 0◦ ( Fig. 12(a) ) have similar modal developments comparing with thesmooth flow ( Fig. 12(b) ). Different modal developments are observed in the gap flow at AoA = −7◦. Theforcing modes (mode(1,1), mode(2,0)),and their second harmonic modes (mode(4,0), mode(2,2)) have the same
trend in streamwise direction as the smooth flow, which indicates the forcing modes are almost not disturbed
by the gap. However, other modes with multiple frequencies and spanwise wave numbers are excited in the gap
and develop downstream. Not only are the modes in Fig. 13(a), other frequencies and spanwise wave numbers
increase rapidly. Among all the modes, the forcing modes, mode(1,1) and mode(2,0), always dominate in the
development which determine the transition onset. This may be the reason why the change of transition onset
by a gap is not obvious.
In order to find out the reason for the gap flow behaviors of different modes, two slices of non-dimensional
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15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
(a) Gap, AoA = 0◦(b) Smooth, AoA = 0◦
Fig. 12 Streamwise velocity disturbance evolution at AoA = 0◦
(a) Gap, AoA =−7◦(b) Smooth, AoA = 0◦
Fig. 13 Streamwise velocity disturbance evolution at AoA =−7◦
pressure fluctuation are plotted in Fig 14. Similar to the longitudinal and transverse mechanisms proposed by
Zhang[11], two feedback mechanisms are observed in the two gap flows with different angles of attack. In the
gap flow at AoA = 0◦, the upstream disturbances propagate towards the aft face of the gap. Most disturbancesdamp at the right corner. As a result, there are no strong disturbance flow out the boundary layer. In contrast,
the disturbance path in the gap flow at AoA = −7◦ is illustrated in Fig. 14(b). There is a single feedback loopin the gap. Disturbances from the boundary layer propagate to the aft face of the gap, flow to the bottom with
the feedback loop and finally transverse back to the boundary layer. According to the experimental results[10],
a longitudinal mechanism exists in a shallow gap and a deep gap leads to a transverse mechanism. The results
in this paper show that a negative angle of attack can also cause a transition from longitudinal to transverse
mode besides the length-to-depth ratio. This may be the reason for the occurrence of the broadband distur-
bance observed in the FFT analysis. Unfortunately, the typical frequencies for the two mechanisms can not
be extracted with the current frequency analysis. A large number of instability waves are produced with this
nonlinear interaction, causing the sudden rise in mode amplitudes, as shown in Fig.13(a).
(a) Pressure fluctuation in gap flow at AoA = 0◦ (b) Pressure fluctuation in gap flow at AoA =−7◦
Fig. 14 Distribution of pressure fluctuation at the slice of z = 0.009m
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15th International Conference on Fluid Control, Measurements and Visualization
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4 Conclusions
Transition processes of a Mach 6 boundary layer with a 2D gap have been studied for two angles of attack,
AoA = 0◦ and AoA = −7◦ with a high order ILES tool, hpMusic, in the present paper. Both 2D and 3Dinstability waves were introduced at the inflow to obtain a subharmonic transition in the simulations. Some
conclusions are drawn next.
In the case of AoA = 0◦, the transition phenomenon of the gap flow is similar to that on smooth one. Theinfluence of the gap occurs mainly in the vicinity of the gap. The flow outside the gap is almost undisturbed.
There is no extra disturbance observed in the gap, and the evolution of the disturbances downstream the gap
is similar to that of the smooth flow. Instability modes propagate toward the aft surface of the gap and damp
rapidly. As a result, little difference is observed in the distribution of skin friction coefficient between gap flow
and smooth flow.
The forcing disturbances show a different interaction with the gap at AoA =−7◦. Transition onset is earlierthan the corresponding smooth one. Three dimensional vortex structure in the gap flow occurs earlier than that
in the smooth flow. According to the FFT analysis, plenty of instability modes other than the forcing modes or
the modes originated from the forcing modes, are observed in the gap and flow downstream which contribute
to transition. A single feedback loop is observed within the gap which is considered to be the reason for the
jump of the broadband modes at the gap.
References
[1] Forte M, Perraud J, Seraudie A, Beguet S, Gentili L, Casalis G (2015) Experimental and Numerical Study
of the Effect of Gaps on Laminar Turbulent Transition of Incompressible Boundary Layers, In:Procedia
IUTAM, Vol. 14, pp 448-458, doi:10.1016/j.piutam.2015.03.073.
[2] Sun Y, Taira K, Cattafesta L, Ukeiley L (2017) Biglobal instabilities of compressible open-cavity flows.
Journal of Fluid Mechanics, vol. 826, pp 270-301. doi:10.1017/jfm.2017.416
[3] Tumin A (2007) Three-dimensional spatial normal modes in compressible boundary layers. Journal of
Fluid Mechanics, vol. 586, pp 295-322. doi:10.1017/S002211200700691X
[4] Duan L, Wang X, and Zhong X (2013) Stabilization of a Mach 5.92 Boundary Layer by Two-Dimensional
Finite-Height Roughness. AIAA Journal, vol. 51(1), pp 266-27. doi:10.2514/1.J051643
[5] Fong K D, Wang X, Zhong X (2014) Numerical simulation of roughness effect on the stability of a hy-
personic boundary layer. Computers & Fluids, vol. 96, pp 350-367. doi:10.1016/j.compfluid.2014.01.009
[6] Sawaya J, Sassanis V, Yassir S, Sescu A, Visbal M (2018) Assessment of the Impact of Two-Dimensional
Wall Deformation Shape on High-Speed Boundary-Layer Disturbances. AIAA Journal, vol. 56(12), pp
4787-4800. doi:10.2514/1.J057045
[7] Marxen O, Iaccarino G, Shaqfeh E S (2014) Nonlinear instability of a supersonic boundary layer with two-
dimensional roughness. Journal of Fluid Mechanics, vol. 752, pp 497-520. doi:10.1017/jfm.2014.266
[8] Tang Q, Zhu Y, Chen X, Lee C (2015) Development of second-mode instability in a mach 6 flat
plate boundary layer with two-dimensional roughness. Physics of Fluids, vol. 27(6), pp 064105.
doi:10.1063/1.4922389
[9] Heller H, Bliss D (1975) The physical mechanism of flow-induced pressure fluctuations in cavities and
concepts for their suppression. In:2nd Aeroacoustics Conference. doi:10.2514/6.1975-491
[10] Kumar M, Vaidyanathan A (2018) Oscillatory mode transition for supersonic open cavity flows. Physics
of Fluids, vol. 30(2), pp 026101. doi.org/10.1063/1.5017269
[11] Zhang X, Edwards J (1990) An investigation of supersonic oscillatory cavity flows driven by thick shear
layers. The Aeronautical Journal, vol. 94(940), pp 355-364. doi:10.1017/S0001924000023319
[12] Rossiter J E (1964) Wind tunnel experiments on the flow over rectangular cavities at subsonic and tran-
sonic speeds. Ministry of Aviation.
Paper ID:312 10
15th International Conference on Fluid Control, Measurements and Visualization
27-30 May, 2019, Naples, Italy
[13] Huynh H T (2007) A Flux Reconstruction Approach to High-Order Schemes Including Discon-
tinuous Galerkin Methods. In: 18th AIAA Computational Fluid Dynamics Conference, pp 4079,
doi:10.2514/6.2007-4079
[14] Wang, Z J, Gao H (2009) A unifying lifting collocation penalty formulation including the discontinuous
galerkin, spectral volume/difference methods for conservation laws on mixed grids. Journal of Computa-
tional Physics, vol. 228(21) pp 8161-8186. doi:10.1016/j.jcp.2009.07.036
[15] Haga T, Gao H, Wang Z J (2011) A high-order unifying discontinuous formulation for the Navier-Stokes
equations on 3D mixed grids. Mathematical Modelling of Natural Phenomena, vol. 6(3), pp 28-56. doi:
doi:10.1051/mmnp/20116302
[16] Wang Z J, Gao H, Haga T (2011) A Unifying Discontinuous CPR Formulation for the Navier-Stokes
Equations on Mixed Grids. In: Kuzmin A. (eds) Computational Fluid Dynamics 2010. pp 59-65, Berlin,
Heidelberg. doi:10.1007/978-3-642-17884-9_5
[17] Huynh H T, Wang Z J, and Vincent P E (2014) High-order Methods for Computational Fluid Dynamics:
a Brief Review of Compact Differential Formulations on Unstructured Grids, Computers & Fluids, Vol.
98(2), pp. 209-220. doi:10.1016/j.compfluid.2013.12.007
[18] Bassi F, Rebay S (2000) A High Order Discontinuous Galerkin Method for Compressible Turbulent Flows.
In: Cockburn B, Karniadakis G E, Shu CW (eds) Discontinuous Galerkin Methods, Berlin, Heidelberg pp
77-88. doi:10.1007/978-3-642-59721-3_4
[19] Sun Y, Wang Z J, Liu Y (2007) Efficient Implicit Non-linear LU-SGS Approach for Viscous Flow Com-
putation using High-Order Spectral Difference Method. In: 18th AIAA Computational Fluid Dynamics
Conference, AIAA Paper, pp 2007-4322. doi:10.2514/6.2007-4322
[20] Li Y, Wang Z J (2017) A convergent and accuracy preserving limiter for the FR/CPR method. In: 55th
AIAA Aerospace Sciences Meeting, AIAA SciTech Forum, pp 0756. doi:10.2514/6.2017-0756
[21] Wang Z J, Li Y, Jia F, Laskowski G M, Kopriva J, Paliath U, Bhaskaran R (2017) Towards indus-
trial large eddy simulation using the FR/CPR method. Computers & Fluids, vol. 156, pp 579-589.
doi:10.1016/j.compfluid.2017.04.026
[22] Egorov I V, Fedorov A V (2006) Soudakov V G. Direct numerical simulation of disturbances generated by
periodic suction-blowing in a hypersonic boundary layer. Theoretical and Computational Fluid Dynamics,
vol. 20, pp 41-54. doi:10.1007/s00162-005-0001-y
[23] Huai X, Joslin R, Piomelli U (1997) Large-Eddy Simulation of Transition to Turbulence in Boundary
Layers. Theoretical and Computational Fluid Dynamics, vol. 9, pp 149-163. doi:10.1007/s001620050037
[24] Fasel H F, Konzelmann U (1990) Non-parallel stability of a flat-plate boundary layer us-
ing the complete Navier-Stokes equations. Journal of Fluid Mechanics, vol. 221, pp 311-347.
doi:10.1017/S0022112090003585
[25] Chang C, Malik M (1994) Oblique-mode breakdown and secondary instability in supersonic boundary
layers. Journal of Fluid Mechanics, vol. 273, pp 323-360. doi:10.1017/S0022112094001965
[26] Ren J, Fu S (2014) Competition of the multiple Gortler modes in hypersonic boundary layer flows. Science
China Physics, Mechanics & Astronomy, vol. 57, pp 1178-1193. doi:10.1007/s11433-014-5454-9
Paper ID:312 11
IntroductionNumerical MethodSimulation results and discussionsConclusions