constructal multi-scale structure for maximal heat transfer density - bejan
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Constructal multi-scale structure for maximal
heat transfer density
A. Bejan, Durham, North Carolina, andY. Fautrelle, Grenoble, France
Received January 3, 2003Published online: June 12, 2003 Springer-Verlag 2003
Summary. This paper presents a new concept for generating the multi-scale structure of a finite-size
flow system that has maximum heat transfer densitymaximum heat transfer rate installed in a fixed
volume. Laminar forced convection and parallel isothermal blades fill the volume. The spacingsbetween adjacent blades of progressively smaller scales are optimized based on constructal theory: the
goal is maximum heat transfer density. The smaller blades are installed in the fresh-fluid regions that
sandwich the tips of the boundary layers of longer blades. The overall pressure difference is con-
strained. As the number of length scales increases, the flow rate decreases and the volume averaged
heat transfer density increases. There exists a smallest (cutoff) length scale below which heat transfer
surfaces are no longer lined by distinct (slender) boundary layers. Multi-scale flow structures for
maximum heat transfer rate density can be developed in an analogous fashion for natural convection.
The constructal multi-scale algorithms are deduced from principles, unlike in fractal geometry where
algorithms are assumed.
1 Geometry
A key result of constructal theory is the prediction of optimal spacings for the internal flow
structure of volumes that must transfer heat and mass to the maximum. This body of work
comprises both forced and natural convection, and is reviewed in [1], [2]. Optimal spacings have
been determined for several configurations, depending on the shape of the heat transfer surface
that is distributed through the volume: stacks of parallel plates, bundles of cylinders in cross-
flow, and arrays of staggered plates. In each configuration, the reported optimal spacing is a
single value, i.e., a single length scale that is distributed uniformly through the available vol-
ume.
Figure 1 shows qualitatively why an optimal spacing exists. The heat-generating blade shown
at the top of the figure is one of many parallel blades that fill a much larger package. Isolated in
Fig. 1 is the volume allocated to a single blade. The size of this volume is fixed, and is repre-
sented by the rectangular space V shown in Fig. 1ac. The shape ofV is not fixed. The fluid
sweeps the blade and convects heat. The boundary layers are regions that work (are active) in a
heat transfer sense. WhenVis considerably wider than the boundary layers (Fig. 1a), most ofV
is occupied by coolant that does not help the heat transfer enterprise. WhenVis much narrower
than the boundary layers (Fig. 1c), most ofVis occupied by thermally fully developed flow, i.e.,
by coolant that warms up in the downstream direction. Such a fluid is overworked, and
becomes poorer as a coolant.
Acta Mechanica 163, 3949 (2003)
DOI 10.1007/s00707-003-1008-3
Acta MechanicaPrinted in Austria
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The best configuration is in-between, Fig. 1b. Here the volume is just wide enough to house
the flow regions that work. The boundary layers merge in the plane of the outlet. This trans-
versal dimension ofV represents the optimal spacing between the parallel blades in the stack.
Three such blades are shown in Fig. 2, whereL0D0has replaced the two-dimensional volumeV
of Fig. 1. The spacingD0is the single length scale that is distributed uniformly through the two-
dimensional flow structure of lengthL0 and widthH. For concreteness, assume laminar forced
convection driven by the imposed pressure difference DP. Assume also that the blades are
isothermal, Tw, and have negligible thickness. Furthermore, the fluid Prandtl number is of
order 1, so that the velocity and thermal boundary-layer thicknesses are both represented by the
Blasius thickness (e.g., [3]),
dx ffi 5x Ux
m
1=2: 1
In this expressionUand m are the free stream velocity and the kinematic viscosity.
Is the stack of Fig. 2 the best way to pack heat transfer into a fixed volume? It is, but only
when a single length scale is to be used, that is, if the structure is to be uniform. The structure of
Fig. 2 is uniform, because it does not change fromx 0 to x L0. At the most, the geometries
of single-spacing structures vary periodically, as in the case of arrays of cylinders and staggered
plates.
The key observation is that the structure of Fig. 2 can be improved if more length scales
(D0;D1;D2;. . .) are available. The technique consists of placing more heat transfer in regions of
the volumeHL0where the boundary layers are thinner. Those regions are situated immediately
downstream of the entrance plane, x 0. This observation is the same as taking the argument
of Fig. 1 to a finer level: regions that do not work in a heat transfer sense must either be put to
work, or eliminated. In Fig. 2, the wedges of fluid contained between the tips of opposing
cold fluid
convective body
V
V
V
heat-generating blade
unused volume
overworked fluid
a
b
cFig. 1. The optimal volume shape for
the flow associated with one blade
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boundary layers are not involved in transferring heat. They can be involved if heat-generating
blades of shorter length (L1) are installed on their planes of symmetry. This new design is shown
in Fig. 3.
Each new L1 blade is coated by boundary layers described by Eq. (1). Becaused increases
as x1/2, the boundary layers of the L1 blade merge with the boundary layers of the L0
blades at a downstream position that is approximately equal to L0/4. The approximation is
due to the assumption that the presence of the L1 boundary layers does not affect signifi-
cantly the downstream development (x > L0/4) of the L0 boundary layers. This assumption
is made for the sake of simplicity. The order-of-magnitude correctness of this assumption is
clear, and it comes from geometry: the edges of the L1 and L0 boundary layers intersect
when
L1 1
4L0: 2
Note that by choosing L1 such that the boundary layers that coat the L1 blade merge with
surrounding boundary layers at the downstream end of theL1 blade, we invoke one more time
the optimal packing principle of Fig. 1. We are consistent, and, because of this, every structure
with merging boundary layers will be optimal, no matter how complicated.
The wedges of isothermal fluid (T0) remaining between adjacent L0 and L1 blades can be
populated with a new generation of even shorter blades, L2 L1/4. Two such blades are shown
in the upper-left corner of Fig. 3. The length scales become smaller (L0,L1,L2), but the shape of
the boundary layer region is the same for all the blades, because the blades are all swept by the
same flow (U). The merging and expiring boundary layers are arranged according to thealgorithm
Li 1
4Li1; Di
1
2Di1 i 1; 2;. . .;m; 3
where we shall see that m is finite, not infinite. In other words, as in all the constructal tree
structures [1], the image generated by the algorithm (3) is not a fractal. It is a Euclidean image
[4], [5]. The sequence of decreasing length scales is finite, and the smallest size (Dm, Lm) is
known, as we will see in Eq. (21).
U, T0, P
0 x L0
TW
D0
Hd(x)
Fig. 2. Optimal package of parallel
plates with one spacing
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To complete the description of the sequential construction of the multi-scale flow structure,
we note that the number of blades of a certain size increases as the blade size decreases. Let n0
be the number ofL0 blades in the uniform structure of Fig. 2,
n0 H
D0; 4
where
D0 ffi 2dL0 ffi 10
mL0
U 1=2
: 5
The number of L1 blades is n1 n0, because there are as many L1 blades as there are D0spacings. At scales smaller thanL1, the number of blades of one size doubles with every step,
ni 2ni1; i 2; 3;. . .;m: 6
Two conflicting effects emerge as the structure grows in the sequence started in Fig. 3. One is
attractive: the total surface of temperatureTw installed in theHL0 volume increases. The other
is detrimental: the flow resistance increases, the flow rate driven by the fixed DPdecreases, and
so does the heat transfer rate associated with a single boundary layer. The important question is
how the volume is being used: what happens to the heat transfer rate density as complexity
increases?
2 Heat transfer
The total heat transfer rate from the Tw surfaces to the T0 fluid can be estimated by
summing up the contributions made by the individual blades. The heat transfer rate through
one side of the L0 blade is equal (in an order of magnitude sense) to the heat transfer rate
associated with a laminar boundary layer, cf. the Pohlhausen solution for Prandtl numbers
of order 1 [3],
D0
L2
L1
L0
D2
D1
0 x Fig. 3. Optimal multi-scale package of
parallel plates
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qq000
DT
L0
k ffi 0:664
UL0
m
1=2: 7
Here qq000
[W/m2] is the L0-averaged heat flux, DT Tw T0, and k is the fluid thermal con-
ductivity. There are 2n0 such boundary layers, and their combined contribution to the totalheat transfer rate of the package of Fig. 3 is
q00
2n0 qq000L0 ffi 1:328kDT n0
UL0
m
1=2: 8
The same calculation can be performed for any group of blades of one size, Li. Their total heat
transfer rateq0i [W/m] is given by a formula similar to Eq. (8), in whichn0 andL0 are replaced
by ni and Li,
q0iffi 1:328kDT niULi
m
1=2: 9
The heat transfer rate of all the blades is the sum
q0 Xmi0
q0iffi 1:328kDT n0UL0
m
1=2
S; 10
whereS is the dimensionless geometric parameter
S 1 n1
n0
L1
L0
1=2
n2
n0
L2
L0
1=2
nm
n0
Lm
L0
1=2
11
or, in view of Eqs. (3) and (6),
S 1 m
2 : 12
This analysis confirms the trend noted at the end of the preceding section: the total heat transfer
rate increases monotonically as the complexity of the structure (m) increases.
3 Fluid friction
It is necessary to evaluate the flow resistance of the multi-scale structure, because the velocityU
that appears in Eq. (10) is not specified. The pressure difference DPis specified, and it is related
to all the friction forces felt by the blades. We rely on the same approximation as in the case of
heat transfer, and estimate the friction force along one face of one blade by using the solution
for the laminar boundary layer (e.g., [3]),
si ffi Cfi1
2qU2; Cfi
1:328
UL0=m 1=2
: 13
Heresiand Cfiare the averaged shear stress and skin friction coefficient, respectively. The total
force felt by the blades of size Li is
Fi 2nisiLiffi 1:328q mLi 1=2
niU3=2: 14
The total force for the multi-scale package is
FXmi0
Fi ffi 1:328q mL0 1=2
n0U3=2S: 15
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This force is balanced by the longitudinal force imposed on the control volume,
DPH F: 16
Finally, by combining Eqs. (15), (16) withn0 H=D0 and the D0 formula (5), we obtain the
order of magnitude of the average velocity of the fluid that bathes the structure:
Uffi 2:7 DP
qS
1=2: 17
This result confirms the second trend anticipated at the end of Sect. 1: the flow slows down as
the complexity of the structure (S, or m) increases.
4 Heat transfer rate density: the smallest scale
Putting together the results of the heat transfer and fluid flow analyses, we find how the
structure performs globally, when its constraints are specifiedDP;DT;H;L0. Eliminating U
between Eqs. (10) and (17) yields the dimensionless global thermal conductance,
q0
kDTffi 0:36
H
L0Be
1=2S1=2; 18
where Be is the dimensionless pressure drop that Bhattacharjee and Grosshandler [6] and
Petrescu [7] termed the Bejan number,
Be DPL2
0
la : 19
In this expressionland aare the fluid viscosity and thermal diffusivity. The alternative to using
the global conductance is the heat transfer rate density, q000 q0=HL0. Both quantities increase
with the applied pressure difference (Be) and the complexity of the flow structure (S). In
conclusion, in spite of the conflicting effects ofS in Eqs. (10) and (17), the effect of increasing S
is beneficial from the point of view of packing more heat transfer in a given volume. Optimized
complexity is the route to maximal global performance in a morphing flow system [1].
How large can the factorSbe? The answer follows from the observation that the geometry of
Fig. 3 and the analyses of Sects. 2 and 3 are valid when boundary layers exist, i.e., when they
are distinct. To be distinct, boundary layers must be slender. Figure 3 makes it clear that
boundary layers are less slender when their longitudinal scales (Li) are shorter. The shortest
blade lengthLm below which the boundary layer heat transfer mechanism breaks down is
Lm Dm: 20
In view of Eqs. (3), this means that
L0 2mD0: 21
Finally, by using Eqs. (5) and (17) we find the smallest scale, which occurs at the levelm given by
2m
1 m
2
1=4 0:17Be1=4: 22
In view of the order-of-magnitude character of the analysis based on Eq. (20), the right side of
Eq. (22) is essentially (Be/103)1/4. Equation (22) establishes m as a slowly varying monotonic
function ofBe1/4. This function can be substituted in Eq. (18) to see the complete effect ofBe on
the global heat transfer performance,
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q0
kDTffi 0:36
H
L0Be
1=21
1
2m
1=2: 23
In conclusion, the required complexity (m) increases monotonically with the imposed pressure
difference (Be). More flow means more length scales, and smaller smallest scales. The structurebecomes not only more complex but also finer. The monotonic effect ofmis such that each new
length scale (m) contributes to global performance less than the preceding length scale (m 1).
If the construction started in Fig. 3 is arbitrarily continued ad infinitum, then the resulting
image is a fractal andm and the heat transfer density (23) tend to infinity.
5 Symmetric growth
Imagine that the blades of the multi-scale structure of Fig. 3 are connected solidly at their
downstream end connected to the neighboring blade of immediately larger scale (see Fig. 4a).
This is certainly not a flow design recommendation, because the fluid must be able to flow
through the structure. It is a useful way to think, because it shows that the population ofLi
blades can be viewed as the branches of a tree structure, and that in this case the tree is
asymmetric. In Fig. 4a, the new (smaller) branches grow on only one side of the tips of the
existing branches.
Nature strikes us with images of tree-shaped structures endowed with symmetry, more like
the drawing shown in Fig. 4b. Here, new branches form on both sides of the tip of an existing
blade. Is this type of growth more advantageous from the point of view of packing maximal
heat transfer into a given volume?
The symmetric-growth alternative to Fig. 3 is shown in Fig. 5. In oneD0 spacing we placed
two L1 blades separated by the distance D1 D0=3. The new boundary layers merge with
neighboring boundary layers whenL1 L0=9. This rule follows from the nonlinear shape of
each boundary layer region, Eq. (1). If the number ofL0 blades in the package is n0, then thenumber ofL1 blades is n1 2n0.
a
b
Fig. 4. Asymmetric (a) versus sym-
metric (b) trees built with blades of
decreasing lengths and increasing
numbers
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The construction can be continued toward smaller scales, by placing two new blades in the
near-entrance region of every spacing. The dimensions of the growing structure follow the
algorithm:
Li1
9Li1; Di
1
3Di1; 24
ni 3i1
2n0 i 1; 2;. . .;ms: 25
The heat transfer and fluid mechanics analyses lead again to Eqs. (10), (11), (15), (17) and (18),
with the difference that Eq. (11) now yields
S 1 2
3ms; 26
wherems is the number of gap filling steps used in the symmetric construction. The subscripts
refers to the symmetric construction of Fig. 5, and is a reminder that the number of con-
struction steps (ms) is not the same as in the asymmetric construction (m), Fig. 3. The number
mscan be determined based on the same argument as in Eq. (20). The smallest blade lengthLmscannot be smaller than
Lms Dms ; 27
whereLms 9msL0and Dms 3
msD0. After using Eq. (5) forD0and Eq. (17) forU, we arrive
at
3ms 1
2
3ms
1=4
Be=1031=4: 28
Equation (28) is plotted in Fig. 6. We see that the complexity (ms) increases as the flow
becomes stronger (i.e., asBe increases). This trend is the same as in the asymmetric structure,
Eq. (22). Furthermore, by comparing Eqs. (28) and (22) when Be is specified, we conclude
that ms < m. The optimal symmetric structure is simpler because it is based on fewer con-
struction steps than the asymmetric structure. The relation between ms and m is roughly
ms=m ln 2= ln 3 0:63, and is only weakly dependent on Be.
The performance of the symmetric structure is given by the same relation as Eq. (23), withSs
in place ofS, namely
q0skDT
ffi 0:36H
L0Be
1=21
2
3ms
1=2; 29
for which the function ms(Be1/4) is furnished by Eq. (28). The performance relative to the
asymmetric case of Eq. (23) is measured by the ratio
L0
D0
D1
L1Fig. 5. Optimal multi-scale package of
parallel plates with two smaller blades
around each larger blade
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q0sq0
ffi 1 2ms=3
1 m=2
1=2
30
which is close to 1, but smaller than 1. The symmetric structure of Fig. 5 is only marginally less
effective than the asymmetric packing of Fig. 3. Figure 6 shows that the ratio q0s=q0 is a function
ofBe, because m and ms are functions ofBe.
6 Conclusions
In this paper, we described a new concept for generating a multi-scale flow structure that
maximizes the heat transfer density installed in a fixed volume. The method consists of ex-
ploiting every available flow volume element for the purpose of transferring heat. In laminar
forced convection, the working volume has a thickness that scales with the square root of the
length of the streamwise heat transfer surface. Larger surfaces are surrounded by thicker
working volumes. The starting regions of the boundary layers are thinner. They are surrounded
by fresh flow that can be put to good use: heat transfer blades with smaller and smaller lengths
can be inserted in the fresh fluid that enters the smaller and smaller channels formed betweenexisting blades.
The number of scales of the multi-scale flow structure (m) increases slowly as the flow
becomes stronger. The flow strength is accounted for by the pressure difference maintained
across the structure (Be). Boundary layers become thinner asBeincreases, and this means that
more small-scale heat transfer blades can be inserted in the interstitial spaces of the entrance
region of the complex flow structure.
Two trends compete as the number of length scales increases. The structure becomes less
permeable, and the flow rate decreases. At the same time, the total heat transfer surface
6
5
4
3ms ms
m m Fig.3
Fig.5
(Be / 103)1/4
(Be / 103)1/4
2
1
01 10 100
1
1
0.95
0.910 100
qs(Fig.5)
qs(Fig.3)
Fig. 6. The number of length scales
(m, ms) as functions of the imposedpressure difference (Be). The bottom
graph shows the relative heat transfer
density of the symmetric vs. asymmet-
ric multi-scale structures
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increases. The net and most important result is that the heat transferdensity increases as the
number of length scales increases. This increase occurs at a decreasing rate, meaning that each
new (smaller) length scale contributes less to the global enterprise than the preceding length
scale. We showed that there exists a characteristic length scale below which heat transfer
surfaces are no longer lined by boundary layers. This smallest scale serves as cutoff for thealgorithm that generates the multi-scale structure.
Forced convection was used in this paper only as a working example, i.e., as a flow mech-
anism on which to build the multi-scale structure. A completely analogous multi-scale structure
can be deduced for laminar natural convection. The complete analogy that exists between
optimal spacings in forced convection and natural convection was described by Petrescu [7]. In
brief, if the structure of Fig. 2 is rotated by 90 counterclockwise, and if the flow is driven
upward by the buoyancy effect, then the role of the overall pressure differenceDPis played by
the difference between two hydrostatic pressure heads, one for the fluid column of height L0
and temperatureT0, and the other for theL0fluid column of temperatureTw. If the Boussinesq
approximation applies, the effectiveDP due to buoyancy is
DP qgbDT L0; 31
where DT is Tw T0, b is the coefficient of volumetric thermal expansion, and g is the
gravitational acceleration aligned vertically downward (againstx in Fig. 2). By substituting the
DP expression (31) into Eq. (19) we find that the dimensionless group that replaces Be in
natural convection is the Rayleigh number
RagbDTL3
0
am : 32
Other than the Be ! Ratransformation, all the features due to the generation of multi-scale
blade structure for natural convection should mirror, at least qualitatively, the features de-
scribed for forced convection in this paper. The heat transfer augmentation effect due to theinsertion of a single plate in the entrance region of the parallel-plates channel was noted and
documented numerically by Aihara et al. [8].
Finally, the flow architecture constructed in this paper is a theoretical comment on fractal
geometry. Fractal structures are generated by assuming (postulating) certain algorithms. In
much of the current fractal literature, the algorithms are selected such that the resulting
structures resemble flow structures observed in nature. For this reason, fractal geometry is
descriptive, not predictive [1], [9]. It is not a theory.
Contrary to the fractal approach, the constructal theory used in this paper generated the
construction algorithms (Eqs. (3), (6), (24) and (25)), including the smallest scale cutoffs, Eqs.
(22) and (28). The algorithms were generated by the constructal principle of optimization of
global performance subject to global constraints [1]. This principle was invoked every time the
optimal spacing between two blades was used. Optimal spacings were assigned to all the lengthscales, and were distributed throughout the volume. With regard to fractal geometry and why
some fractal structures happen to resemble natural flow structures, the missing link has been
the origin of the algorithm [10]. Constructal theory delivers the algorithm as an optimization
result, from the constructal principle [1].
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J. Heat Mass Transfer 37, 1283 (1994).
[8] Aihara, T., Ohara, T., Sasaco, A., Akaku, M., Gori, F.: Augmentation of free-convection heat
transfer between vertical parallel plates by inserting an auxiliary plate. 2nd European Thermal-
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Authors addresses: A. Bejan, Department of Mechanical Engineering and Materials Science, Duke
University, Box 90300, Durham, North Carolina, NC 27708-0300, U.S.A.; Y. Fautrelle, Institut
National Polytechnique de Grenoble, EPM-MADYLAM Laboratory ENSHMG, B.P. 95, 38402 Saint
Martin dHeres Cedex, France
Multi-scale structure for maximal heat transfer density 49