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EFFECTS OF ROTATION ON FLOW IN A RIB-ROUGHENED CHAN-
NEL: LES STUDY
D. Borello1, F. Rispoli1, A. Salvagni1, and K. Hanjalic2
1Dipartimento di Ingegneria Meccanica e Aerospaziale, Sapienza Università di Roma, Italy 2Delft University of Technology, the Netherlands, and Novosibirsk State University, Russia
Abstract.
We report on large-eddy simulations of fully-
developed flow in a duct of a rectangular cross-
section in which square-sectioned, equally-spaced
ribs, oriented perpendicular to the flow direction,
were mounted on one of the walls. The duct was sub-
jected to clock-wise (stabilizing) and anti-clock-wise
(destabilizing) rotation. We analyzed the effects of
stabilizing and destabilizing rotation on the flow, its
vortical structures and turbulence statistics by com-
paring results with non-rotating case.
1 Introduction
The quest for increasing gas-turbine cycle effi-
ciency by rising the turbine inlet temperature poses
ever new challenges to the design of blade cooling
system (e.g. Saravanamuttoo et al., 2001). Among
various methods, the internal cooling enhanced by
turbulence promoters (pins, ribs, grooves) inside the
blades has proved to be both convenient and effi-
cient. A number of studies of flow and heat transfer
in passages with turbulence promoters can be found
in the literature, but less is known about the effect
of rotation on the flow, vortical and turbulence
structures and heat transfer in such configurations.
Among various options for passive enhancement
of heat transfer, rib-roughened channels and ducts
appear especially popular because of their generic
and simple configuration and straightforward repro-
ducibility both experimentally and computationally.
Several experimental and computational studies ap-
peared recently in the literature dealing with flow
and heats transfer in ribbed ducts of a similar con-
figurations. Tafti (2005) reported on LES of flow
and heat transfer in a non-rotating rectangular duct
with the opposing walls roughened with square-
sectioned ribs at Re=20.000. The focus of the analy-
sis was the role and effect of different subgrid-scale
(sgs) models in predicting the flow and heat trans-
fer. He concluded that dynamic Smagorinsky sgs re-
turns better predictions (here compared with
MILES), and that a 1283 discretisation (about 2.1M
cells) is sufficient for obtaining wall-resolved LES.
Abdel-Wahab and Tafti (2004) performed LES of
flow and heat transfer in the same ribbed duct sub-
jected to rotation. Different rotational numbers (up
to 0.67) were studied. These authors observed that
turbulence and heat transfer was augmented in the
trailing side (destabilizing), whereas the opposite
effect was detected in the leading side (stabilizing)
region. The origin of the heat transfer enhancement
and depression was traced in the influence of the
Coriolis force on the various components of the
Reynolds stress tensor through the production term
related to rotation. It is recalled that the rotational
“production” term in the Re-stress equation is trace-
less, thus it has a redistributive character and it does
not appear in the turbulent kinetic energy nor scale-
providing (scalar) equations. For this reason, the
first-moment (linear eddy viscosity) URANS mod-
els are not appropriate for solving flows with sys-
tem rotation. As for the velocity field Abdel-Wahab
and Tafti (2005) reported that in the rotating cases,
in the trailing (destabilizing) region the recircula-
tion bubble is weakly shrunk, and after a threshold
value it is not reduced at all. On the opposite, on the
leading (stabilizing) region the length of the recircu-
lation region increases with the angular velocity
eventually extending over the most of the region be-
tween the two successive ribs. Another effect of the
Coriolis force is the generation of secondary, coun-
ter-rotating flow cells in the duct cross section af-
fecting the shear layer and consequently the heat
transfer on the smooth walls.
Recently Coletti et al. (2011) reported on exper-
imental investigation of the influence of rotation on
the flow over a rib-roughened wall in a duct of a
rectangular cross-section at the bulk Reynolds num-
ber of 1.5 x 104. Ten square-sectioned, equally
spaced ribs aligned with the rotation axis were
mounted on one of the walls. In addition to the non-
rotating situation, both the clock-wise (stabilizing)
and anti-clockwise (destabilizing) rotation were
considered at the rotation number of 0.3, using the
PIV technique. The measurements were reported for
only for the vertical mid-plane.
This paper reports on large-eddy-simulations of
the Coletti et al. (2011) flows, aimed at providing
additional information that were not measured or
are inaccessible to the experiments. We attempt to
gain some new insights into the effect of stabilizing
and destabilizing rotation with focus on the region
over the ribs.
2 Flow and computational details
Coletti et al. (2011) observed that the flow be-
comes periodic after the 6th rib. We focussed thus on
solving the fully-developed periodic flow at
Re=15,000 mimicking the experiment, and used for
verification the PIV data obtained between 6th and 7th
rib. The solution domain was thus xyz=
100.951.05, where the dimensions are expressed in
hydraulic diameters Dh. The rib height h is equal to
1/10 of Dh. The computational domain is meshed us-
ing an unstructured hexahedral orthogonal grid. The
grid was refined in the region y<2h, where the wake
of the rib is relevant. Three grids were considered:
3.5, 5.8 and 8.8106 (M) cells. The finest grid was
created from the intermediate one by increasing the
refinement in the wake region and the number of grid
points in the spanwise direction (Fig.1).
The LES of the case with clockwise (stabilizing)
rotation showed satisfactory results with the interme-
diate grid, while the other two cases require a finer
meshing. In fact, the non-rotating flow showed to be
most grid-sensitive and satisfactory predictions were
obtained only when using the finest grid. The coun-
ter-clockwise case on the intermediate grid showed a
fair comparison with the experiments, though still not
fully satisfactory. For a fair comparison, the case
with counter-clockwise rotation is currently being
recomputed on the finest grid. The results here re-
ported refers to the intermediate grid (5.8 M) for the
two rotating cases and to the fine grid (8.8M) for the
non-rotating flow.
The grid refinement close to the wall allows to
achieve the wall-nearest y+ value (of the first row of
cells) always smaller than 0.5 (the height of the first
cells row was 0.002 compared with the hydraulic di-
ameter, being roughly 2% of the rib height).
The quality of the grid discretisation is illustrated
in Fig. 2. The first subfigure 2a shows the ratio of the
characteristic LES (sgs) length scale =(xyz)1/3
and the Kolmogorov length scale 3 1/4( / ) in the
mid-span plane for the 5.8 M grid. The scale was
computed using the dissipation rateobtained from a
RANS computation with the k--f model (not dis-
cussed here). The scale ratio is never greater than 10
and it is smaller than 5 in most of the relevant region.
Moreover, the power spectra in Fig 2.b at 6 different
points in the mid-plane show that the resolved grid
scales are well beyond the inertial (-5/3) sub-range.
Finally, the grid spacing for the 8.8 M cells, normal-
ised with the rib height, is depicted in Fig.2.c. The
grid density is very high around the ribs, where x/h
andy/h are always lower than 510-3. In the rest of
the domain the ratio never exceeds 1.510-2. These
values demonstrate that the used discretization is al-
ways finer than the one used by Tafti (2005) for the
LES of non-rotating rib-roughened grid at
Re=20,000. The grid discretization used for the 5.8
M grid (not shown here), shows near-wall spacing
similar with that used by Tafti (2005).
Periodic boundary conditions are set at the inlet
and outlet cross-sections. On the solid walls no-slip
conditions are imposed. The non-dimensional time
step was set equal to 10-4, to maintain the CFL num-
ber always lower than 0.3.
The subgrid-scale (sgs) motion was modelled us-
ing the dynamic Smagorinsky approach. No correc-
tion was included in the sgs model to account for the
rotational effects.
The governing equations, non-dimensionalized by
the hydraulic diameter Dh, the bulk flow velocity and
standard air properties, were solved by the well-
validated in-house unstructured finite-volume com-
putational code T-FlowS from TU Delft (Ničeno and
Hanjalić, 2004), now advanced in Sapienza Universi-
tà di Roma. The code has been used successfully for
LES computations of a variety of flows and heat
transfer (e.g. Delibra et al. 2010, Borello et al. 2013).
A second-order accurate CDS scheme is used for
the discretization of the convection and diffusion
terms. The time integration was carried out using also
a second-order scheme. The velocity and pressure
were coupled using the SIMPLE scheme. The linear-
ized algebraic system of the discretized equations
was solved using the Preconditioned BiCG solver.
The threshold for the global mass balance residu-
al was set to 10-6, while for the momentum and con-
tinuity equations it was 10-7. Simulations were per-
formed on the ENEA-Cresco3 and on CINECA-
Eurora supercomputers using up to 64 cores.
About 40 wall clock hours are required for per-
forming 1 flow-through-time (FTT). After an initial
development interval (equal to 2 FTT), the simula-
tions were averaged over 25 FTT for the clockwise-
rotating case and 15 FTT for the other cases.
3 Results and Discussion
3.1 Time-averaged results
The blockage effect of the rib causes the flow to
accelerate and subsequently to expand after the ob-
stacle. In the centre of the duct the flow is nearly
two-dimensional in the bulk, but with several vortical
systems clearly identifiable: a leading edge vortex at
the rib-wall junction, a large recirculation region be-
hind the rib with a small counter-rotating vortex at
the base of the rib, a recirculation region on the rib
tip, and a recovering boundary layer after reattach-
ment. All these structures are captured in all the LES
computations, Fig.3, in agreement with Abdel-
Wahab and Tafti (2004).
Table 1 compares the recirculation lengths for
the three cases considered, obtained by the present
LES, the experiments of Coletti et al. (2011) and the
LES of Abdel-Wahab and Tafti (2004) at Re=20,000
and Ro=0.18.
Table 1 – Length of the recirculation bubble Bubble length Stab. Non-rot Destab.
Exp 5.65 3.85 3.45
LES 5.60 3.90 3.50
Abdel-Wahab and Tafti ~7.00 4.0 3.6
A broader picture of the velocity field is given in
Fig 3, showing the time-averaged streamlines and
coloured mean velocity field in the vertical mid-
plane. To expose the effect of rotation in the rib-wall-
adjacent area, only a fraction of the cross-section is
shown for y/h<3.0. The LES and PIV plots show fair
agreement for all the configurations considered. As
seen, system rotation strongly affects the flow as a
whole, but the major effect appears in the recircula-
tion regions behind the rib. Presumably, this is in part
due to the direct effect of the bulk Coriolis force in
the momentum equation on the separated shear layer
that would be sensed also in laminar flow, but also by
the indirect contribution of the fluctuating Coriolis
force to the production/redistribution terms in the
Reynolds stress equation. The latter affects the level
of different component of the turbulent stress tensor.
In the destabilizing case the shear layer is pushed up-
stream towards the wall thus contributing to an early
reattachment (Fig. 3.b). The opposite occurs for the
stabilizing rotation (Fig.3c), where the recirculation
bubble is stretched and the recirculation length ex-
tends over more than 60% of the surface between the
two successive ribs. This structure modification will
have a strong effect on heat transfer, as a larger
amount of fluid trapped in the recirculating region
will get heated and lose the capacity to remove heat
from the adjacent wall.
Remarkably, rotation seems to have little effect
on the small bubble in front of the rib, though the
stabilizing rotation shows visibly earlier separation
than in the destabilizing case.
Figure 4 shows a comparison of the LES-
computed mean velocity profiles with the experi-
mental data of Coletti et al. (2011). The latter are
available only for the region close to the ribbed wall.
For an overall impression, Fig. 4 shows also a sketch
of the whole flow configuration with typical flow
patterns and main vortical systems. The agreement
between the computed and measured profiles at five
streamwise locations for all three cases considered
can be regarded as satisfactory. In fact the stabilizing
and the non-rotating cases were reproduced very well
and the destabilizing case reasonably well. The stabi-
lized rotation makes the profiles less turbulent and
the opposite occurs for the destabilizing rotations.
The LES returns very satisfying results especially in
predicting the recirculating boundary layer in the first
measurement sections and the successive develop-
ment downstream from the reattachment point.
Secondary motions pertinent to flows in square-
sectioned ducts play a significant role in removing
fluid (and heat) from the walls. The effects of the
side walls are depicted in Figs 5 and 6, showing the
axial velocity profiles over the whole flow in three
stream-wise vertical cross-sections placed at the
channel mid-plane (z/Dh=0.0), close to one of the
side walls (z/Dh=0.45, the wall being at z/Dh=0.475)
and in a plane in between (z/Dh=0.3) for the non-
rotating flow and for the destabilizing rotation. Three
streamwise locations were considered: at the down-
stream edge of the rib (x/h=0), at the end of the recir-
culation bubble (x/h=4), and in the boundary layer
recovering region (x/h=8).
A common feature of both cases is that, when
moving away from the near rib region (i.e. y/h>0.3),
the velocity profile remains more or less the same at
all streamwise locations considered.
In the non-rotating case (Fig.5) the influence of
the secondary motion is clearly evident. Close to the
lower wall the secondary motions induced by the rib
transport fluid towards the smooth walls. Then, at
z/Dh=0.3 where the influence of smooth wall is weak,
the streamwise velocity is higher compared with the
velocity at z/Dh=0.0. For the same reason, for y/h>0.5
the velocity at z/Dh=0.3 is lower than at the center-
line. Closer to the smooth wall (z/Dh=0.45), the
streamwise velocity is dumped by the lateral bounda-
ry layers.
In the destabilizing case (Fig.6), the increase in
the turbulence level is evident. The boundary layer is
thinner and the velocity distribution much more uni-
form across the channel height. Also in this case, at
y/h=0.3 the velocity is greater than at the centerline.
To illustrate the flow pattern close to the ribs and
in the region in between, the velocity and streamline
distribution in two planes parallel to the lower wall,
(y/h=0.05 and 0.5) are shown in Fig. 7.
Close to the wall (y/h=0.05), the destabilizing ro-
tation results in shrinking of the recirculation bubble,
while the stabilizing rotation produced an opposite
effect, i.e. the bubble elongation. Furthermore, in the
non-rotating case, the recirculation bubble has a
‘bow’ shape reaching the minimum extension close
to the smooth walls (i.e. for maximum and minimum
z values) and increasing when moving toward the
mid-span. On the opposite, in the rotating cases the
presence of secondary flows makes the recirculation
bubble more uniform. The small eddy formed below
the recirculation bubble is also subjected to shrinking
(or extension) when destabilizing (or stabilizing) ro-
tation is imposed. Similar features are noticed in the
plane at the rib mid-height (y/h=0.5).
Fig. 8 show mean velocity field in a flow-normal
cross-section, here at x/h= 4.5. In the non-rotating
flow, Fig.8a shows very regular two structures divid-
ed vertically, whereas the destabilizing Coriolis force
greatly distorts, but strengthens this motion (Fig 8.b
and 8.c) relative to the axial velocity. It is worth not-
ing that in the destabilizing case, the two vortical
structures placed close the two smooth walls are sim-
ilar to the two eddies that are noticed in a rotating
square duct (Fig.8.d). In this simplified case, the vor-
tical structures are also present close to the trailing
surface too, though of a simpler topology (see also
Abdel-Wahab and Tafti, 2004).
Some example of the second-moment statistics
for the non-rotating and destabilizing rotating flows
are shown in Figs 9 and 10. In general the LES re-
sults show a similar qualitative trends as the experi-
ments, though agreement is not fully satisfactory, es-
pecially further downstream at the location x/h=8.
Admittedly, more sampling is needed for gathering
statistics, but the discrepancy could be attributed to
the insufficiently long solution domain (only one pe-
riod); we are currently running the same cases in a
twice longer solution domain encompassing the
length of two rib periods. Nevertheless, an indication
of the strong flow three-dimensionality and of the ef-
fects of the side wall can be envisaged from profiles
shown in the vertical mid-plane and two laterally
displaced planes, all parallel to the flow direction (at
z/Dh=0.0, 0.3 and 0.45). Likewise, the turbulence en-
hancement due to destabilizing rotation is clearly vis-
ible in both figures. Needless to say that the stabiliz-
ing rotation dampens all turbulent stress components
(not shown here).
3.2 Flow unsteadiness
Some illustrations of the instantaneous velocity
and streamlines are given by selected snapshots of
the whole solution domain in Fig.11. In the non-
rotating case the high velocity appears in the core of
the flow (at about y/h=4), where periodic peaks ap-
pear roughly midway between the ribs. Multiple
spanwise vortical rolls appear behind the rib, with
their width exceeding the rib height and thus con-
tracting the flow cross-section. It is symptomatic that
the above mentioned velocity peaks appear roughly
at the positions of the maximum roll thicknesses.
This very unsteady flow is rich on turbulent activity,
but the streamlines remain confined without deliver-
ing fluid into the outer main flow. Similar pattern is
evident also in the clockwise rotation, but here the
rolls are much smaller, less vigorous and less turbu-
lent. The external flow shows smooth and almost un-
deformed streamlines, testifying of the rotation stabi-
lizing effect. High velocity flow is moved toward the
upper wall under the influence of the Coriolis force.
In contrast, in the anti-clockwise rotation case, a vig-
orous turbulence is visible not only close to the
ribbed wall but also in the bulk flow, indicating at a
stronger mixing and momentum (and supposedly also
heat) exchange. The streamlines indicate that fluid is
removed from the wall-adjacent regions towards the
core. Here, the Coriolis force pushes the core of high
velocity to deflect towards the ribbed wall. Similar
effects have been detected in planes close to the lat-
eral (side) wall (not shown here)
4 Conclusions
LES of flow in a rectangular-sectioned ribbed
duct, subjected to stabilizing and destabilizing system
rotation, have been conducted aimed at gaining a fur-
ther insight into the effects of rotation on flow, vorti-
cal and turbulence structures. The simulations were
verified against the PIV measurements in a character-
istic plane. The analysis shows that the destabilizing
(anti-clockwise) rotation enhances turbulence pro-
duction along the ribbed wall, enhances the lateral
mixing and strengthens the secondary motion, which
all enhance momentum (and, presumably, also heat)
transfer. In contrast, the stabilizing Coriolis force
make the whole flow less turbulent, the effects being
especially noticeable in the vicinity of the bottom
ribbed wall (pressure-side). These effects are ex-
pected to profoundly influence heat transfer, the topic
currently studied.
Secondary motions pertinent to flows in rectan-
gular-sectioned ducts play a significant role in re-
moving fluid (and heat) from the walls. Rotation (as
well as ribs and flow separation) modify their struc-
tures. In the non-rotating flow, two very regular
structures appear, being clearly divided vertically. In
contrast, the destabilizing Coriolis force greatly dis-
torts, but strengthens this motion relative to the axial
velocity.
As in turbine blades ribs are placed usually on
both sides of the interior cavities, both rotation cases
are relevant for the practical design of gas-turbine
blade cooling.
References
Abdel-Wahab, S. and Tafti, D. K. 2004, Large eddy
simulation of flow and heat transfer in a 90° ribbed
duct with rotation – Effect of Coriolis forces, Turbo-
Expo 2014, June 14-17, Wien, Austria.
Borello, D., Salvagni, A., Rispoli, F. and Hanjalic, K.
(2013) LES of the flow in a rib-roughened duct,
DLES 9, 3-5 April, 2013, Dresden, Germany
Coletti, F., Maurer, T., Arts, T. & Di Sante, A.
(2011), Flow field investigation in rotating rib-
roughened channel by means of particle image veloc-
imetry, Exp. Fluids, 54(9), n.1589.
Delibra, G., Borello, D., Hanjalic, K. and Rispoli, F.
(2010), Les of flow and heat transfer in a channel
with a staggered cylindrical pin matrix, Direct and
Large-Eddy Simulation VII, Springer.
Tafti, D. K. (2005), Evaluated the role of subgrid
stress modelling in a ribbed duct for the internal cool-
ing of turbine blades, Int. J. Heat and Fluid Flow,
Vol. 26, pp. 92-104.
Niceno, B. and Hanjalic, K. (2004), Unstructured
large-eddy and conjugate heat transfer simulations of
wall-bounded flows, in Modeling and Simulation of
Turbulent Heat Transfer, WIT Press. 3573.
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H., 2001, Gas Turbine Theory, 5th Edition, Prentice
Hall.
a) b)
Fig. 1: Grid discretisation - details of the cross planes: a) 5.8 Million cells; b) 8.8 Million cells
Fig. 2: Assessment of the quality of the LES predictions: left – ratio in the mid plane center – energy spectra;
right variation of the grid spacing (for the finer grid).
Non-rotating
Destabilizing rotation
Stabilizing rotation
Fig. 3: Comparison of LES and PIV streamines and velocity field (colour-bar) in the central vertical plane: left non-
rotating; center stabilizing; right: destabilizing. Remark: non-rotating configuration has finer grid (8.8M cells)
Fig. 4: Top left: sketch of the flow configuration (from Coletti et al. 2011). Mean streamwise velocity profiles at x/h
LES
=0, 2, 4, 6 and 8: Symbols: experiments (PIV, Coletti et al. 2011); lines: present LES.
Fig. 5: Non-rotating case. Mean streamwise velocity profiles at x/h =0, 4 and 8: Symbols: experiments (PIV, Coletti et
al. 2011); lines: LES.
Fig. 6: Destabilizing case. Mean streamwise velocity profiles at x/h =0, 4 and 8: Symbols: experiments (PIV, Coletti et
al. 2011); lines: LES.
Non-rotating
Destabilizing rotation
Stabilizing rotation
Fig. 7: Velocity and streamlines in two planes parallel to the lower (rib-roughened) wall: top y/h=0.05; bottom: y/h=0.5
a
b
c.
d.
Fig. 8 Mean velocity in the the y-z plane at x/h=4.5: a-no rotation, b-clockwise, c-anti-clockwise; d:
rotating square duct (different velocity scale)
Ω=0
Ω>0
Ω=0
Ω>0
Fig. 9: The streamwise (top) and wall-normal (bottom) turbulence intensity component for the non-rotating (Ω=0) and
destabilizing rotating case (Ω>0). Symbols: Experiments (Coletti et al, 2011). Lines: simulations. Chain line: z/D=0,
full line: z/D=0.3, dotted line: z/D=0.45
Ω=0
Ω>0
Fig. 10: Turbulent shear stress component uv for the non-rotating (Ω=0) and destabilizing rotating case (Ω>0). Sym-
bols: Experiments (Coiletti et al, 2011). Lines: simulations. Chain line: z/D=0, full line: z/D=0.3, dotted line: z/D=0.45
Fig. 11: Instantaneous streamlines and velocity profiles at mid-plane for the three configurations: left –non-rotating;
centre – clock-wise; right – anti-clockwise
a
b
c
Fig. 12 Instantaneous velocity field in the y-z plane at x/h=4.5: a-no rotation, b-
clockwise, c-anti-clockwise