ORIGINAL
Natural convection in inclined two dimensionalrectangular cavities
Lyes Khezzar • Dennis Siginer • Igor Vinogradov
Received: 9 May 2010 / Accepted: 25 July 2011
� Springer-Verlag 2011
Abstract Steady two-dimensional natural convection in
fluid filled cavities is numerically investigated. The chan-
nel is heated from below and cooled from the top with
insulated side walls and the inclination angle is varied. The
field equations for a Newtonian Boussinesq fluid are solved
numerically for three cavity height based Rayleigh num-
bers, Ra = 104, 105 and 106, and several aspect ratios. The
calculations are in excellent agreement with previously
published benchmark results. The effect of the inclination
of the cavity to the horizontal with the angle varying from
0� to 180� and the effect of the startup conditions on the
flow pattern, temperature distribution and the heat transfer
rates have been investigated. Flow admits different con-
figurations at different angles as the angle of inclination is
increased depending on the initial conditions. Regardless of
the initial conditions Nusselt number Nu exhibits discon-
tinuities triggered by gradual transition from multiple cell
to a single cell configuration. The critical angle of incli-
nation at which the discontinuity occurs is strongly influ-
enced by the assumed startup field. The hysteresis effect
previously reported is not always present when the
calculations are reversed from 90� to 0�. A comprehensive
study of the flow structure, the Nu variation with varying
angle of inclination, the effect of the initial conditions and
the hysteresis effect are presented.
List of symbols
A Surface area (m2)
AR Aspect ratio (=L/H)
g Gravitational acceleration (m/s2)
H Height of cavity
L Width of cavity
Nu Nusselt number
p Pressure (N/m2)
Pr Prandtl number
Ra Rayleigh number based on the height H of the cavity
TH Hot wall temperature
TC Cold wall temperature
T Fluid temperature
u, v Flow velocity components in x and y directions
respectively (m/s)
Greek symbols
b Fluid expansion coefficient (K-1)
/ Angle of inclination (deg)
j Thermal diffusivity of fluid (m2/s)
m Kinematic viscosity (m2/s)
q Fluid density (kg/m3)
w Stream function
1 Introduction
Natural convection in enclosures is important in applica-
tions such as materials processing, solar energy systems,
inclined flat plate solar collectors, nuclear energy systems,
L. Khezzar (&)
Department of Mechanical Engineering, Petroleum Institute,
Abu Dhabi, United Arab Emirates
e-mail: [email protected]
D. Siginer
Centro de Investigaciones en Creatividad y Educacion Superior,
Universidad de Santiago de Chile, Santiago, Chile
I. Vinogradov
Department of Mechanics and Aerospace Engineering,
Peking University, Beijing 100871, People’s Republic of China
123
Heat Mass Transfer
DOI 10.1007/s00231-011-0876-7
double-glazed window heat transfer, electronic cooling and
food sterilization. Literature for free convection in rectan-
gular enclosures has been reviewed by Gebhart et al. [1],
Ostrach [2] and recently Khalifa [3]. The work of
Ayyaswamy and Catton [4] and Clever [5] both published
the same year in 1973 are the first investigations to our
knowledge of this flow configuration. Ozoe et al. [6]
experimentally investigated and numerically computed
values of the Nusselt number for natural convection heat
transfer in a square channel with two inclined sides
maintained isothermally hot and cold and the other two
sides insulated. Complex flow patterns appear as the angle
of inclination decreases to less than 10� which suggests the
possibility of multiple, stationary flow modes. However, as
the inclination approaches zero degree a series of two-
dimensional roll-cells with their axes horizontal and per-
pendicular to the axis of the channel are eventually attained
as the stable flow mode. The maximum rate of heat transfer
is obtained both theoretically and experimentally at about
50� of inclination, whereas the minimum heat transfer rate
was experimentally found to occur at an inclination of
about 10� from the horizontal.
Ozoe et al. [7] presented both numerical and experi-
mental studies in two dimensional rectangular channels
with four different aspect ratios ranging from 1 to 4. The
maximum rate of heat transfer occurs at an angle of
inclination of 60� (bottom heated). The minimum rate of
heat transfer occurs at a small angle of inclination, and it is
a moderate function of aspect ratio and a slight function of
Ra. A change in the mode of circulation was observed
when the heat transfer rate reaches the minimum value.
The circulation pattern for angles of inclination below this
point of transition is observed to be a series of oblique roll-
cells. The computed values of average Nu showed general
agreement with experimental results except at small angles
of inclination for which a different mode of circulation
prevailed. Experimental measurements of heat transfer
rates were reported by Ozoe and Sayama [8] for laminar
natural convection of silicone oil and air in a long rect-
angular channel with aspect ratios of 1, 2, 3, 4.2, 8.4, 15.5,
and Rayleigh numbers ranging from 3 9 103 to 105 and
findings similar to [7].
Catton et al. [9] and Arnold et al. [10] investigated
experimentally and numerically heat transfer in inclined
cavities for a range of aspect ratios, Rayleigh numbers and
angles of inclinations. Heat transfer rates due to natural
convection in rectangular bottom heated regions inclined at
various angles from 0� to 180� with four different aspect
ratios from 1 to 12 were measured for Rayleigh numbers
between 103 and 106 by Arnold et al. [10] and a simple
scaling law valid for angles of inclination from 0� to 90�defining the relationship of Nu with the angle of inclination
and Ra was derived. Karayiannis and Tarasuk [11] studied
natural convection inside a rectangular cavity with differ-
ent temperature boundary conditions on the cold top plate
using a Mach–Zehnder interferometer. Correlation equa-
tions for coupled and non-coupled average heat transfer
rates are presented.
The transition of flow modes was also studied numeri-
cally by Soong et al. [12] who note the influence of initial
conditions on the flow pattern formation in a cavity of
aspect ratio of 4 and for a range of Rayleigh numbers from
1,500 to 20,000. For a horizontal cavity heated from below
of aspect ratio equal to 3, the flow pattern was found to be
strongly influenced by the initial conditions; however the
average Nusselt number remained unaffected. Corcione
[13] with horizontal cavities of several aspect ratios and
using numerical techniques considers the effect of bi-
directional differential heating at Rayleigh numbers
between 103 and 106 and conjectures that the increase in
the number of roll cells as the aspect ratio increases may be
explained through the progressive breakdown of the den-
sity stratification in the fluid layers adjacent to the top and
bottom walls affecting the formation of hot and cold fluid
streams moving upward and downward across the cavity
and thereby shaping the temperature distribution. Flow
mode transition and hysteresis phenomena for Rayleigh
numbers greater than 3,000 were demonstrated in [12] as
well as by Wang and Hamed [14] who conducted a sys-
tematic numerical study of the variation of the Nusselt
number with angle of inclination for a range of Rayleigh
numbers from 103 up to 104 and a single aspect ratio of 4.
They considered in addition to adiabatic side walls, the
effect of bi-directional temperature gradients on the side
walls and concluded that these types of flows could have
dual or multiple solutions and attributed them to initial
condition effects. The discontinuity in the Nusselt number
variation with angle of inclination and the hysteresis phe-
nomenon mentioned previously were observed for steady
as well as unsteady calculations under the Boussinesq
approximation [12–14].
Clearly for differentially heated two-dimensional
enclosures in one direction and adiabatic side walls, the
heat transfer characteristics are influenced by the inclina-
tion of the cavity with respect to the horizontal plane, the
thermal boundary conditions and the Rayleigh number
based on the height of the cavity. However, despite the
studies conducted so far on rectangular cavity flows with
varying Rayleigh and Prandtl numbers and aspect ratios,
several aspects of the phenomenon remain to be clarified,
for instance the maximum Nusselt number with varying
angle of inclination usually thought to be around 50�, the
presence and location of the Nusselt number discontinuity
related to the flow structure and the ensuing circulation
mode change, as well as the hysteresis phenomenon and the
effect of the initial conditions.
Heat Mass Transfer
123
Against this background a comprehensive numerical
investigation of the steady buoyancy induced flow in an
inclined two dimensional rectangular cavity of a Newto-
nian fluid with linear Boussinesq density-temperature
dependence is conducted in this paper. Constant surface
temperatures on two opposite walls are maintained at a
fixed differential value with the other two walls insulated.
The interest is focused on the dynamic and thermal aspects
of a two-dimensional cavity heated from below and cooled
from the top with the other two sides being insulated when
the cavity is inclined over the horizontal from 0� to 180�, in
other words the heating starts from below at 0� and ends
from above when the angle of inclination is 180�. Several
cavity aspect ratios are investigated, with three Rayleigh
numbers of 104, 105 and 106 for a linear fluid with a Prandtl
number of 10. Cavity flows are known to depend on initial
assumed fields, Hart [15] and Soong et al. [12], even in
steady flow computations and thus the investigation of the
combined effects of initial start up field conditions and
angle of inclination on the flow structure and the heat
transfer together with the hysteresis effect is the subject of
the present work. In particular, the present work expands
on the combination of aspect ratios and Rayleigh numbers
considered thus far and focuses on the idea of the effect of
initial conditions to consider for each angle of inclination a
zero start up field in addition to the previously used
approach of taking the solution at the preceding angle as
the start up field in seeking the solution for the subsequent
angle. Whenever possible and in order to provide the
necessary confidence, the computational results are com-
pared with a number of previously published numerical and
experimental results with the latter confined to the average
Nusselt number.
2 Mathematical formulation
A two dimensional rectangular cavity filled with a New-
tonian fluid is considered. The assumption of two dimen-
sional flow is adequate in most cases to simulate the flow
and heat transfer even in three dimensional cavities as edge
effects remain small, Bairi et al. [16]. The inclination angle
of the cavity / varies between 0� B / B 180�. The aspect
ratio is AR = L/H, the ratio of the length L of the iso-
thermal walls to the length H of the adiabatic walls. The
top (cold) and the bottom (hot) surfaces of the cavity are
maintained at constant temperatures Tc and Th while the
two side walls are kept adiabatic as shown in Fig. 1. Flow
in the cavity is assumed laminar, steady and two-dimen-
sional. The steady form of the conservation equations for
this type of flow has been previously used [13, 14, 16]. It is
known that for horizontal (zero inclination) cavities the
onset of convection is expected around the critical
Rayleigh number of 1708, Holland and Raithby [17].
Beyond this critical value the flow may quite possibly
exhibit multiple solutions around the same Ra. However,
grid independence tests and solutions obtained with
increasing angles starting at a finite 1� angle rather than
zero for AR = 3 and Ra = 104 confirm the approach
adopted (see discussion at the end of Sect. 3). Boussinesq
approximation holds, viscous dissipation is assumed to be
negligible, and all other fluid properties are assumed con-
stant. The buoyancy force is caused only by the density
gradient, thus:
qq0
¼ 1� b T � T0ð Þ ð1Þ
where b is the coefficient of thermal expansion,
b = 7.0 9 10-5 (�K)-1 for water, q is the fluid density
at temperature T, q0 and T0 are the corresponding reference
values, respectively. The field conservation equations of
mass, momentum and energy are given by:
ou
oxþ ov
oy¼ 0 ð2Þ
uou
oxþ v
ou
oy¼ � 1
qop
oxþ m
o2u
ox2þ o2u
oy2
� �þ gb T � T0ð Þsin/
uov
oxþ v
ov
oy¼ � 1
qop
oyþ m
o2v
ox2þ o2v
oy2
� �þ gb T � T0ð Þcos/
ð3Þ
uoT
oxþ v
oT
oy¼ j
o2T
ox2þ o2T
oy2
� �ð4Þ
The area-averaged Nusselt number on the conducting
walls is calculated using:
Nu ¼ 1
A
ZA
0
oT
oy
������wall
dx ð5Þ
The velocity vector is expressed in terms of its Cartesian
components (u, v) along the x and y directions of the
coordinate system shown in Fig. 1; p, m, j and g represent
the pressure, the kinematic viscosity, the thermal
diffusivity and the acceleration of gravity, respectively.
The Rayleigh and Prandtl numbers are defined as,
y x
HL
φ
TC
Th
g
Fig. 1 Flow geometry
Heat Mass Transfer
123
Ra ¼ gb Th � Tcð ÞH3
mj; Pr ¼ m
jð6Þ
The set of Eqs. 2–4 is solved numerically using the
finite volume technique and the Fluent code on a Cartesian
grid with grid sizes that ensure grid-independent solutions.
The grid independence issue is explored in depth in the
next section with important observations. Convective terms
are discretized using the Quick Scheme, see [18], since for
structured meshes this scheme has greater formal accuracy
and central differencing is used for the diffusion terms
discretization. The SIMPLE algorithm is used for velocity–
pressure coupling and since a co-location scheme is used
PRESTO is adopted for pressure interpolation at cell faces
and is known to perform well for high Rayleigh number
natural convection flows [19]. On the walls zero slip
conditions are prescribed for the momentum equations.
Constant temperatures are prescribed for heated and cooled
walls and zero heat flux for the side adiabatic walls.
Convergence was assumed when the normalized residuals
reached a value of 10-4 in monitoring appropriate field
variables. For some configurations near zero angle of
inclination of the cavity no convergence was obtained and
therefore for these angles solutions are not reported.
Grid independence tests were performed using three
grids for the square cavity for the three Rayleigh numbers
adopted and for the angle of inclination of 90� as shown in
Table 1. The intermediate grid in each case was used since
the solution obtained is very close to the solution for the
finest grid based on a comparison of the Nusselt numbers
and stream function values. In addition, the benchmark
results for the square cavity with side walls at constant
temperatures and the top and bottom walls insulated of De
Vahl Davis [20] were used to test the calculations for a
Prandtl number of 0.7 and for Ra = 104, 105 and 106. The
maximum deviation of the calculated Nusselt numbers from
the benchmark values was less than 1%. For the rectangular
configurations again three grids were chosen as shown in
Tables 2 and 3 for two Rayleigh numbers Ra = 105 and 106
and an angle of inclination of 25� and 90�. The intermediate
angle of 25� was chosen because at this angle the flow
contains a multi-cell structure and hence represents a more
stringent case for grid independence. It is assumed that
the grid used for Ra = 105 will also be valid for Ra = 104.
The intermediate grids in Tables 2 and 3 were used for the
calculations and are appropriate for the purpose of the
present work based on the comparisons of the Nusselt
numbers and stream function values. The results are also
compared when possible with experimental and numerical
results found in the literature for the rectangular and square
cavities as will be shown in the next section.
For each cavity aspect ratio and Rayleigh number,
calculations are carried varying the angle of inclination in
three ways. In the first set, the computations are started
from zero velocity field conditions and reference tem-
perature T0 at zero angle of inclination and the solution
obtained is used as a subsequent initial condition for the
next angle and so on. The step increase in the angles is 5�between 0� and 90�, larger step angles are used beyond
90�. In the second set of calculations, a solution is sought
for each angle starting from an initial zero field condition
and reference temperature T0, while the third set of cal-
culations starts from an angle of 90� and proceeds back-
wards by decreasing the angle to reach the horizontal
position. In the latter in a similar fashion to the first set,
the results of each angle are used as start up conditions for
the next angle.
3 Results and discussion
Calculations were performed for Pr = 10 and three Ray-
leigh numbers of 104, 105 and 106 for several aspect ratios
and the results reported are discussed considering the effect
of the Rayleigh number, aspect ratio, the initial conditions
and the hysteresis effect on the average Nusselt number on
the active walls and the flow structure.
Figures 2, 3, 4, and 5 show the variation of the average
Nusselt number on the conducting walls with angle of
inclination and Rayleigh number for four aspect ratios
AR = 1, 3, 6 and 12. Each figure shows three sets of data,
the filled dots are the results obtained assuming zero field
start up conditions for each angle and the square dots show
the result of calculations done using the computed solution
at the previous angle of inclination as a startup field. The
third set of data shown by the empty triangles illustrate the
results of calculations obtained using the solution at 90� as
an initial start-up field and reversing the sequence of cal-
culations by decreasing the angle from 90� until the cavity
regains its horizontal 0� position.
Figure 2 shows the variation of Nu with angle of incli-
nation for AR = 1 the square cavity. Nu increases mono-
tonically to reach a maximum value of around 2.44, 4.92
and 9.71 with increasing Ra at an angle between 65 and
70�. There is no difference between computational results
the two sets of initial conditions described above yield. For
Ra = 106 convergence is elusive for inclinations below 3�.
The residuals oscillate around a value without ever reach-
ing the convergence levels mentioned above. The absolute
maximum of Nu occurs at about 60� for AR in the neigh-
borhood of AR = 1. At any aspect ratio AR the absolute
maximum of Nu grows with growing Ra and tends to occur
at an angle slightly larger at increasingly larger Ra. How-
ever at the same Ra with increasing AR the Numax shows
considerable decrease, Figs. 2, 3, 4, and 5. The variation of
Numax is more strongly dependent on Ra than it is on AR.
Heat Mass Transfer
123
Conversely the dependence on AR is weaker as compared
to the dependence on Ra.
For AR = 3, 6 and 12, Figs. 3, 4, and 5, and when
Ra = 104 and 105 the dependence of Nu on / is quite
different. Nu shows an aspect ratio and Ra dependent dis-
continuity and computations using different sets of initial
conditions yield different behavior and discontinuities that
take place at different angles of inclination. The compu-
tational results with either set are in complete agreement
before and after the discontinuities. The agreement past the
latest discontinuity is clearly due to the flow configuration
in this region which is single cell for calculations corre-
sponding to either set of start-up conditions. With zero
start-up conditions the flow configuration switches at a
smaller inclination angle to a single cell configuration and
with continuous initial conditions the single vortex gets
established at a greater angle of inclination, i.e it is
delayed, Figs. 6, 8, 9, 11. The critical angle at which the
vortices merge to become a single cell is Ra and AR
dependent. Keeping Ra constant the critical angle grows
with growing aspect ratio AR regardless of the initial
conditions used to compute the field. With both initial data
set and with increasing / Nusselt number Nu reaches a
local maximum after which it drops suddenly to a lower
value. For Ra = 104 the step change in Nu for continuous
flow computations takes place at angles 40�, 45� and 50�whereas for Ra = 105 it occurs at 40�, 50� and 47� for
AR = 3, 6 and 12 respectively. For the zero initial field
Table 1 Grid independence tests AR = 1 and / = 90�
Ra Grid Nu (% Dev.) wmax (% Dev.)
104 100 9 100 2.2680 3.2% 0.00078436 8.2%
150 9 150 2.2081 0.51% 0.00072036 -0.60%
300 9 300 2.1970 (-) 0.00072473 (-)
105 100 9 100 4.5550 -0.09% 0.00156345 1.0%
150 9 150 4.5597 0.02% 0.00154844 0.06%
300 9 300 4.5590 (-) 0.00154753 (-)
106 150 9 150 9.1000 0.14% 0.00284406 1.4%
200 9 200 9.1330 0.51% 0.00278972 -0.57%
300 9 300 9.0870 (-) 0.00280562 (-)
Table 2 Grid independence
tests Ra = 105 and / = 90� and
/ = 25�
AR Grid Nu (% Dev.) wmax (% Dev.)
Angle = 90�3 150 9 150 4.0980 -0.36% 0.003486 0.11%
250 9 100 4.0970 -0.39% 0.003484 0.06%
300 9 300 4.1130 (-) 0.003482 (-)
6 150 9 150 3.5769 -0.30% 0.006182 0.00%
250 9 100 3.5765 -0.31% 0.006185 0.05%
300 9 300 3.5876 (-) 0.006182 (-)
12 200 9 160 3.0737 -0.50% 0.010234 0.11%
250 9 150 3.0800 -0.30% 0.010225 0.02%
500 9 300 3.0892 (-) 0.010223 (-)
Angle = 25�3 150 9 150 4.3 0.77% 0.00713 -0.97%
250 9 100 4.31 1.01% 0.00727 0.97%
300 9 300 4.267 (-) 0.0072 (-)
6 150 9 150 4.3607 3.90% 0.00737 -2.25%
250 9 100 4.1906 -0.15% 0.0076 0.80%
300 9 300 4.197 (-) 0.00754 (-)
12 200 9 160 4.352 2.16% 0.00758 -4.44%
250 9 150 4.26018 0.00% 0.00776 -2.17%
500 9 300 4.26 (-) 0.007932 (-)
Heat Mass Transfer
123
Table 3 Grid independence
tests Ra = 106 and / = 90� and
/ = 25�
AR Grid Nu (% Dev.) wmax (% Dev.)
Angle = 90�3 150 9 100 7.6281 0.31% 0.006383 0.19%
200 9 100 7.6291 0.32% 0.006385 0.22%
300 9 200 7.6048 (-) 0.006371 (-)
6 300 9 50 6.6232 1.67% 0.01096 1.28%
200 9 100 6.5445 0.46% 0.010848 0.25%
400 9 200 6.5146 (-) 0.010821 (-)
12 200 9 70 3.0737 -0.50% 0.01835 0.27%
250 9 100 3.0800 -0.30% 0.0183 0.00%
400 9 140 3.0892 (-) 0.0183 (-)
Angle = 25�3 150 9 100 6.6960 1.27% 0.00934 -2.20%
200 9 100 6.6490 0.56% 0.00968 1.36%
300 9 200 6.6120 (-) 0.00955 (-)
6 300 9 50 5.6647 0.51% 0.01096 -4.70%
200 9 100 5.69338 1.02% 0.0114 -0.87%
400 9 200 5.636 (-) 0.0115 (-)
12 200 9 150 4.7079 0.17% 0.0168 -1.18%
250 9 100 4.6896 -0.22% 0.01677 -1.35%
500 9 300 4.7000 (-) 0.017 (-)
Fig. 2 Variation of Nu when
AR = 1 with / (open squarenon-zero startup field, filledcircle zero startup field)
Heat Mass Transfer
123
Fig. 3 Variation of Nu when
AR = 3 with / (open squarenon-zero startup field, filledcircle zero startup field)
triangles indicate decreasing
angle calculations from 90� to
0�
Fig. 4 Variation of Nu when
AR = 6 with / (open squarenon-zero startup field, filledcircle zero startup field),
triangles indicate decreasing
angle calculations from 90� to
0�
Heat Mass Transfer
123
computations, the step change for Ra = 104 occurs at an
approximate angle of 12� for AR = 3 and 6� and 15� for
AR = 12, whereas for Ra = 105 the discontinuity takes
place at 9.5�, 11� and 12� for AR = 3, 6 and 12. Consid-
ering only one set of initial conditions results, it can be
seen that as Ra is changed its effect on angle of mode
transition is barely noticeable. For all aspect ratios the drop
in Nu seems to be much attenuated for continuous field
startup conditions with the size of the steep drop in Nu
about 1/3 of the size of the earlier occurring drop resulting
from the zero initial condition computations. For all aspect
ratios when Ra = 106 and in particular for AR = 3 and 12
the step change in Nu moves closer to 0� with increased
size. For AR = 12, Ra = 106 there is a steep drop in Nu
from a value of 6–4 starting in the very neighborhood of 0�with zero initial condition computations whereas continu-
ous field initial condition computations seem to indicate a
rise in Nu from 6 to 6.5 and then dropping steeply to 4.75 at
about 15�. This behavior is in line with previous findings
[10, 12]. In all cases the maximum Nu gets smaller with
decreasing Ra at a given AR and the discontinuity in Nu
seems to move closer to 0�. For Ra = 106, except for
AR = 12 convergence problems were experienced for
angles less or equal than 4� and thus results for these angles
are not shown.
The sudden drop of Nu with angle of orientation has
been observed previously in [10] and [12] and is due to the
transition of the flow cell structure from multiple cells to a
single cell. The multi-cell structure which prevails at 0�(Benard flow) is gradually modified with increasing /through a series of cascading configurations with a smaller
number of cells culminating in a final single cell in the
enclosure. Stream function and temperature contours nor-
malized by the local corresponding maximum values for
Ra = 105 and AR = 6 and AR = 3 at different angles of
inclination for continuous start-up conditions are illustrated
in Figs. 6 and 9. For AR = 6, as the angle is increased the
initial multi-cell pattern of 6 cells observed at 0� gradually
shifts to a lower number of cells in stages, a structure with
5 cells between 20� and 35� followed by a three cell con-
figuration at about 45�. The multiple cell structure further
bifurcates into a single-cell around 55� associated with a
discontinuity in the Nu. The single cell mode prevails
thereafter until the angle of inclination reaches 180�whereby the mode of heat transfer is conduction dominated
as implied by the isotherms for 170�, Fig. 7. Figure 8
shows the stream function evolution for the same angles as
those of Fig. 6 for zero initial conditions. The discontinuity
in Nu and consequently the gradual evolution of the flow
structure from multiple cell to single cell occurs at a much
earlier angle of inclination around 12�. The flow patterns at
55� and 170� are very much similar. For AR = 3 the cell
pattern starts with 4 unequal cells shifting to 3 cells
between 20� and 40� and at 45� the pattern bifurcates to a
Fig. 5 Variation of Nu when
AR = 12 with / (open squarenon-zero startup field, filledcircle zero startup field);
triangles indicate decreasing
angle calculations from 90� to
0�
Heat Mass Transfer
123
single cell which prevails until the inclination reaches
180�, Fig. 9. The temperature contours of Fig. 10 associ-
ated with the multi cell structures are similar to the ones
depicted in Fig. 7 for AR = 6. The particular angle at
which a flow mode transition occurs depends upon the
Rayleigh number as evidenced by Figs. 3, 4, and 5. The
evolution of the field with increasing angle / with zero
initial conditions for the same aspect ratio is shown in
Fig. 11. The flow structure from multiple cell to single cell
occurs at much earlier inclination of 12� as compared to the
computations with continuous start-up conditions, Figs. 9
and 10.
In all the cases investigated the initial number of cells
depends upon the Rayleigh number and aspect ratio in line
with the findings of Corcione [13]. A single cell pattern
prevails after the last transition until 180�. Flow and tem-
perature fields are symmetric about the central vertical
plane for 0� and about the central horizontal plane when
the angle is 90�. Multiple cell flow configurations create
upward and downward convecting cold and hot streams.
The temperature contours of Figs. 7 and 9 show alternating
compression and spreading of isotherms near the bottom
and top conducting walls implying a varying heat flux in a
wavy manner on these walls.
Calculations were performed in reverse, starting with
the calculated field at 90� and gradually decreasing the
angle of inclination to reach the horizontal position of 0�.
The results of these computations are illustrated in Figs. 3,
4, and 5 for AR = 3 to AR = 12. These calculations were
conducted to investigate the hysteresis phenomenon
observed in [12, 14] and thought to be related to the multi
solution nature of this flow due to the effects of the starting
flow fields during the numerical integration of the conser-
vation equations. The hysteresis phenomenon was not
observed for AR = 3 for all Ra and for AR = 6 for
Ra = 105 and 106. In these cases where it is absent, the
Fig. 6 Stream function contours at inclination / for AR = 6 and
Ra = 105; non-zero startup field, Nx = 250 and Ny = 100Fig. 7 Temperature contours at inclination / for AR = 6 and
Ra = 105; non-zero startup field, Nx = 250 and Ny = 100
Heat Mass Transfer
123
Nusselt number decreased monotonically until 0� was
reached without showing any discontinuity, and the single
cell flow structure obtained at 90� persists all the way to
angle 0�. When hysteresis was present Nu decreased with
decreasing angle and exhibited a discontinuity to reach a
lower value at 0� than the one calculated with the
increasing angle computations. The jump in Nu is associ-
ated with the change in the flow mode with the appearance
of multiple roll cells. For both cases, the variation of Nu
coincided exactly with the values obtained with increasing
angle computations between 90� and the angle where either
discontinuity took place. The reasons behind this behavior
are difficult to ascertain since it is not clear what exactly
causes the transition between one flow mode and the other.
The variation of Nu with aspect ratio and Ra for an
inclination of 90� that is with vertical active walls and
horizontal adiabatic walls is shown in Fig. 12. Nu for each
Ra increases to a maximum value for an aspect ratio around
one and thereafter decreases monotonically with AR. As
expected Nu is a strong function of Ra for this orientation,
with higher Ra achieving higher heat transfer rates. The
calculated Nu values agree very well with the experimental
values of Arnold et al. [10] when AR = 1, 6 and 12 and the
Fig. 8 Stream function contours at inclination / for AR = 6 and
Ra = 105; zero startup field, Nx = 250 and Ny = 100
Fig. 9 Stream function contours at inclination / for AR = 3 and
Ra = 105; non-zero startup field, Nx = 250 and Ny = 100
Heat Mass Transfer
123
computed values of Catton et al. [9]. This serves to confirm
the reliability of the present computational results. On the
same graph the experimental correlations of Catton [21].
Equations 7–9 are also plotted. It can be seen that there is
very good agreement between Eq. 8 and the calculation
results when 2 \ AR \ 10 with an average error of about
2%. For AR = 1 the results reported for the three Rayleigh
numbers considered agree to within 1–2% with the calcu-
lations of Bairi et al. [16]. When AR is between 1 and 2 the
agreement is still good between the calculations and Eq. 7
for Ra = 104 and Ra = 105 but the calculations over pre-
dict the correlation values for the third Rayleigh number,
the average error in this case is around 4%. Beyond
Fig. 10 Temperature contours at inclination / for AR = 3 and
Ra = 105; non-zero startup field, Nx = 250 and Ny = 100
Fig. 11 Stream function contours at inclination / for AR = 3 and
Ra = 105; zero startup field, Nx = 250 and Ny = 100
Heat Mass Transfer
123
AR = 10 the numerical calculations continue to exhibit a
decrease of the Nusselt number with AR and under predict
the correlation values that show an increase beyond
AR = 10 with an average error of about 15%.
Nu ¼ 0:18Pr
0:2þ PrRa
� �0:29 1\ LH \2
10�3\Pr\105
103\ Ra Pr0:2þPr
8<: ð7Þ
Nu ¼ 0:22Pr
0:2þ PrRa
� �0:28L
H
� ��0:25
2\ LH \10
Pr\105
103\Ra\1010
8<:
ð8Þ
Nu ¼ 0:42Ra0:25Pr0:012 L
H
� ��0:3 10\ LH \40
1\Pr\2� 104
104\Ra\107
8<:
ð9Þ
Figure 13 shows the variation of Nu with aspect ratio for
Ra = 104 and 105 when the angle of orientation is 0�. Nu
increases rapidly between AR = 0 and 1 and thereafter
gradually to tend asymptotically to a constant value in a
similar fashion to horizontal air layers equal to the unique
value reported in the numerical simulations of Corcione
[13] for Ra = 105. The actual fit with the correlation Nu ¼0:21 ARð Þ0:09
proposed by Corcione [13] and developed for
aspect ratios between 0.66 and 8 and a range of Rayleigh
numbers between 104 and 106 is very good specially for
Ra = 104 and with a maximum local discrepancy for
Ra = 105 less than 5%. It can hence be extrapolated with
confidence to aspect ratios up to 12.
4 Conclusions
The buoyancy induced flow with linear density-tempera-
ture dependence in a two dimensional rectangular cavity is
investigated numerically for angles of inclinations between
0� and 180�. Flow configuration and heat transfer behavior
due to natural convection in enclosures of aspect ratios
1, 3, 6 and 12 for Ra = 104, 105 and 106 and Pr = 10 are
determined.
The results are consistent and in very good agreement
with experimental and simulation data in the literature.
However this investigation goes far beyond the existing
studies and probes aspects of this flow configuration hith-
erto unexplored. The behavior in Nu and in particular the
sudden decrease in average heat transfer as the angle is
increased in the first quadrant is associated with the cas-
cading flow changes leading from a multiple cell configu-
ration in the neighborhood of 0� to configurations with
gradually decreasing number of cells ending up with a
single cell structure thereafter leading to more and more
conduction dominated heat transfer mode as the angle of
inclination approaches 180�. The critical angle of inclina-
tion at which the discontinuity occurs is strongly influenced
by the assumed startup field. It was found that previously
reported hysteresis phenomenon is not always present.
The computations also revealed that the transition to a
single cell structure associated with the sudden drop in the
Nu depends upon the assumed startup field. Assuming a
zero startup field leads to an earlier transition towards a
single cell structure. However, the solutions obtained with
different initial conditions are in full agreement when both
reach the single cell mode. Although the results are
repeatable, it is somehow difficult to explain this behavior
Fig. 12 Variation of Nu with AR when / = 90�, lines represent
correlations of Eqs. 7–9 and empty symbols are taken from Ref. [8, 9]
Fig. 13 Variation of Nu with AR when / = 0�, lines indicate
correlation Nu = 0.21(AR)0.09 of [13]
Heat Mass Transfer
123
except to stress that by its very nature, the multi cell flow is
complex not stable and sensitive to orientation of the cavity
and hence would tend to show sensitivity to the initial
conditions in the process of changing from a multi cell to a
single cell structure.
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