UFR 2-12 Test Case

Turbulent Flow Past Two-Body Configurations

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Test Case Study

Brief Description of the Study Test Case

A detailed description of the chosen test case (TC with L = 3.7D) is available at this link. So here we present only its brief overview.

A schematic of the airflow past the TC configuration is shown in Figure 1. The model is comprised of two cylinders of equal diameter aligned with the streamwise flow direction. The polar angle, ${\theta }$, is measured from the upstream stagnation point and is positive in the clockwise direction.

Figure 1: Schematic of TC configuration [3]

Geometric and regime parameters defining the test case are summarized in Table 1.

Table 1: Flow parameters

Parameter	Notation	Value
Reynolds number	Re=$U_{0}D/\nu$	1.66×105
Mach number	M	0.128
Separation distance	$L/D$	3.7
TC aspect ratio	$L_{z}/D$	12.4
Cylinder diameter	$D$	0.05715 m
Free stream velocity	$U_{0}$	44 m/s
Free stream turbulence intensity	$K$	0.1%

The principal measured quantities by which the success or failure of CFD calculations are to be judged are as follows:

• Mean Flow
  • Distributions of time-averaged pressure coefficient, $C_{p}\leq (p-p_{0})\geq (1/2\rho _{0}U_{0}^{2})$, over the surface of both cylinders;
  • Distribution of time-averaged mean streamwise velocity ${\left.\langle u\rangle /U_{0}\right.}$ along a line connecting the centres of the cylinders;
• Unsteady Characteristics
  • Distributions of the root-mean-square (rms) of the pressure coefficient over the surface of both cylinders;
  • Power spectral density of the pressure coefficient (dB/Hz versus Hz) on the upstream cylinder at $\theta$ = 135°;
  • Power spectral density of the pressure coefficient (dB/Hz versus Hz) on the downstream cylinder at $\theta$ = 45°;
• Turbulence kinetic energy
  • x – y cut of the field of time-averaged two-dimensional turbulent kinetic energy ${\text{TKE}}={\frac {1}{2}}\left(\langle u'u'\rangle +\langle \nu '\nu '\rangle \right)/U_{0}^{2}$;
  • 2D TKE distribution along* y = 0;
  • 2D TKE distribution along* x = 1.5 D (in the gap between the cylinders);
  • 2D TKE distribution along* x = 4.45 D (0.75 D downstream of the centre of the rear cylinder).

All these and some other data are available on the web site of the BANC-I Workshop.

Test Case Experiments

A detailed description of the experimental facility and measurement techniques is given in the original publications [2-4] and available on the web site of the BANC-I Workshop. So here we present only concise information about these aspects of the test case.

Figure 2: TC configuration in the BART facility [3]

Experiments have been conducted in the Basic Aerodynamic Research Tunnel (BART) at NASA Langley Research Center (see Figure 2). This is a subsonic, atmospheric wind-tunnel for investigation of the fundamental characteristics of complex flow-fields. The tunnel has a closed test section with a height of 0.711 m, a width of 1.016 m, and a length of 3.048 m. The span size of the cylinders was equal to the entire BART tunnel height, thus resulting in the aspect ratio L_z / D = 12.4. The free stream velocity was set to 44 m/s giving a Reynolds number based on cylinder diameter equal to 1.66 × 10⁵ and Mach number equal to 0.128 (flow temperature T = 292 K).

The free stream turbulence level was less than 0.10%. In the first series of the experiments [2, 3], in order to ensure a turbulent separation from the upstream cylinder at the considered Reynolds number, the boundary layers on this cylinder were tripped between azimuthal locations of 50 and 60 degrees from the leading stagnation point using a transition strip. For the downstream cylinder, it was assumed that trip-like effect of turbulent wake impingement from the upstream cylinder would automatically ensure turbulent separation. However, later on [4] it was found that the effect of tripping of the downstream cylinder at L/D = 3.7 is also rather tangible (resulted in reduced peaks in mean C_p distribution along the rear cylinder, accompanied by an earlier separation from the cylinder surface, a reduced pressure recovery, lower levels of mean TKE in the wake and reduced levels of peak surface pressure fluctuations). For this reason, exactly these (with tripping of both cylinders) experimental data [4] were used for the comparison with fully turbulent CFD.

In the course of experiments, steady and unsteady pressure measurements were carried out along with 2-D Particle Image Velocimetry (PIV) and hot-wire anemometry used for documenting the flow interaction around the two cylinders (mean streamlines and instantaneous vorticity fields, shedding frequencies and spectra).

Information on the data accuracy available in the original publications [2-4] is summarized in Table 2. Most absolute values are given based on nominal tunnel conditions or on an average data value. Percentage values are quoted for parameters where the uncertainty equations were posed in terms of the uncertainty relative to the nominal value of the parameter.

Table 2: Estimated Experimental Uncertainties

Quantity	Uncertainty
Steady Cp	0.02
Drag Coefficient	0.0005
PIV: Umean, Vmean	0.03 (normalized)
PIV: Spanwise velocity	1.8 (normalized)
PIV: TKE	4%
Power Spectral Density (PSD)	10 – 20%
Cp' rms	5 – 11%
Diameter, D; Sensor spacing Δz	0.005 inch

CFD Methods

The key physical features of the UFR (Section 1) present significant difficulties for all the existing approaches to turbulence representation, whether from the standpoint of solution fidelity (for the conventional (U)RANS models) or in terms of computational expense for full LES (especially if the turbulent boundary layers are to be resolved). For this reason, most of the computational studies of multi-body flows, in general, and the TC configuration, in particular, are currently relying upon hybrid RANS-LES approaches. This is true also with regard to simulations carried out in the course of the BANC-I and II Workshops and in the framework of the ATAAC project, where different hybrid RANS-LES models of the DES type were used (see Table 3) .

Table 3: Summary of simulations

Partner	Turbulence Modelling approach	Compressible/Incompressible	Lz	Grid	Side Walls
Beijing Tsinghua University BTU	SST DDES	Compressible	3D	Mandatory	Slip
German Aerospace Center, Göttingen DLR	SA DDES	Compressible	3D	Mandatory	Slip
New Technologies and Services, St.-Petersburg, Russia NTS	SA DDES SA IDDES	Incompressible and Compressible	3D, 16D	Mandatory	Slip
Technische Universität Berlin TUB	SA DDES SA IDDES	Incompressible	3D	Mandatory	Slip
SST - k–ω Shear Stress Transport model [9]; SA - Spalart-Allmaras model [10]; SA and SST DDES - Delayed DES based on the SA and SST models [11]; SA IDDES - Improved DDES based on the SA model [12].

As mentioned in the experiments section above, in the experiments the boundary layers on both cylinders were tripped ahead of their separation, thus justifying the "fully turbulent" simulations.

All the partners used their own flow solvers.

Particularly, BTU employed in-house compressible Navier-Stokes code with weighted, central-upwind, approximation of the inviscid fluxes based on a modification of the high-order symmetric total variation diminishing scheme. The method combines 6th order central and 5th order WENO schemes. For the time integration, an implicit LU-SGS algorithm is applied with Newton-like sub-iterations.

   *DLR*  used  their  unstructured  TAU   code   with   a   finite   volume
   /compressible/  Navier-Stokes  solver.  The  solver  employs  a  standard
   central scheme with matrix dissipation with dual time stepping strategy
   of Jameson. The 3W Multi-Grid cycle was applied for  the  momentum  and
   energy equations, whilst the SA transport equation was  solved  on  the
   finest grid only. Time  integration  was  performed  with  the  use  of
   explicit 3-level Runge-Kutta scheme. The method is of the 2nd order  in
   both space and time.

   *NTS* used in-house NTS finite-volume  code.  It  is  a  structured  code
   accepting   multi-block   overset   grids   of   Chimera   type.    The
   /incompressible/ branch of the code employs Rogers and Kwak  scheme  [13]
   and  for  /compressible/  flows  Roe  scheme  is  applied.  The   spatial
   approximation of the inviscid fluxes within these methods is  performed
   differently  in  different  grid  blocks  (see  Figure  3  below).   In
   particular, in the outer block, the 3rd-order upwind-biased  scheme  is
   used,  whereas  in  the  other  blocks,  a  weighted  5th-order upwind-
   biased/4th-order central  scheme  with  automatic  (solution-dependent)
   blending function [14] is employed. For the time integration,  implicit
   2nd-order backward Euler scheme with sub-iterations was applied.

   Finally, *TUB* applied their in-hose multi-block structured code ELAN  in
   the framework of  the  /incompressible/  flow  assumption.  The  pressure
   velocity coupling is based on the SIMPLE algorithm. For the  convective
   terms a hybrid approach [15] with blending  of  2nd-order  central  and
   upwind-biased TVD schemes was used. The time integration was similar to
   that of NTS.

   The viscous terms of the governing  equations  in  all  the  codes  are
   approximated with the 2nd order centered scheme.

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Contributed by: A. Garbaruk, M. Shur and M. Strelets — New Technologies and Services LLC (NTS) and St.-Petersburg State Polytechnic University

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