ELSEVIER
Heat Transfer and Pressure Drop Correlations
for the Rectangular Offset Strip Fin
Compact Heat Exchanger
Raj M. Manglik
Department of Mechanical, Industrial and Nuclear
Engineering, University of Cincinnati,
Cincinnati, Ohio
Arthur E. Bergles
Department of Mechanical Engineering,
Aeronautical Engineering and Mechanics,
Rensselaer Polytechnic Institute,
Troy, New York
• The development of thermal-hydraulic design tools for rectangular offset
strip fin compact heat exchangers and the associated convection process
are delineated. On the basis of current understanding of the physical
phenomena and enhancement mechanisms, existing empirical f and j data
for actual cores are reanalyzed. The asymptotic behavior of the data in the
deep laminar and fully turbulent flow regimes is identified. The respective
asymptotes for f and j are shown to be correlated by power law expressions
in terms of Re and the dimensionless geometric parameters a, 6, and y.
Finally, rational design equations for f and j are presented in the form of
single continuous expressions covering the laminar, transition, and turbu-
lent flow regimes.
Keywords: enhanced heat transfer, compact heat exchangers, offset
strip fins, thermal-hydraulic performance, heat exchanger design
INTRODUCTION
Compact heat exchangers are used in a wide variety of
applications. Typical among these are automobile radia-
tors, air-conditioning evaporators and condensers, elec-
tronic cooling devices, recuperators and regenerators, and
cryogenic exchangers. The need for lightweight, space-
saving, and economical heat exchangers has driven the
development of compact surfaces. The modem automo-
bile radiator perhaps best exemplifies the advancement
and technological development in compact heat exchang-
ers since its vintage predecessor of the early 1900s. In
recent times the thrust for energy conservation and the
use of alternative energy resources has extended their
application to ocean thermal energy conversion, solar, and
geothermal systems [1].
Compact heat exchangers are generally characterized
by extended surfaces with large surface area/volume ra-
tios that are often configured in either plate-fin or tube-fin
arrangements [2]. In a plate-fin exchanger, which finds
diverse applications, a variety of augmented surfaces are
used: plain fins, wavy fins, offset strip fins, perforated fins,
pin fins, and louvered fins [2]. For these complex geome-
tries, which are usually set up in a cross-flow arrangement,
few predictive models or generalized correlations are
available [2, 3], and actual databases are often employed
for design. Though containing relatively old data, the
monograph by Kays and London [4] is perhaps the most
comprehensive design sourcebook. Design issues have also
been addressed in several reviews by Dubrovsky [5], Shah
et al. [6], Shah and Webb [2], and Shah [7, 8].
Of the many enhanced fin geometries described earlier,
offset strip fins are very widely used. They have a high
degree of surface compactness, and substantial heat trans-
fer enhancement is obtained as a result of the periodic
starting and development of laminar boundary layers over
uninterrupted channels formed by the fins and their dissi-
pation in the fin wakes. There is, of course, an associated
increase in pressure drop due to increased friction and a
form-drag contribution from the finite thickness of the
fins. Typically, many offset strip fins are arrayed in the
flow direction, as schematically shown in Fig. 1. Their
surface geometry is described by the fin length l, height h,
transverse spacing s, and thickness t. The fin offset is
usually uniform and equal to a half-fin spacing; a nonuni-
form offset will introduce an additional geometrical vari-
able. Furthermore, manufacturing irregularities such as
burred edges, bonding imperfections, and separating plate
roughness also influence the flow and heat transfer char-
acteristics in actual heat exchanger cores.
There has been considerable effort to understand
the convection mechanisms and to predict the thermal-
hydraulic behavior in offset strip fin cores, and it contin-
ues to attract much research attention [9-12]. The many
reported studies include experimental data for actual cores
or scaled-up models, empirical correlations, flow visualiza-
tion, mass transfer data, analytical models, and numerical
Address correspondence to Dr. Raj M. Manglik, Department of Mechanical, Industrial and Nuclear Engineering, University of Cincinnati,
Cincinnati, OH 45221-0072.
Experimental Thermal and Fluid Science 1995; 10:171-180
© Elsevier Science Inc., 1995
655 Avenue of the Americas, New York, NY 10010
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SSDI 0894-1777(94)00096-Q
172 R.M. Manglik and A. E. Bergles
r.-8~
a = s lh
t h 6 = t / t
,y = t ls
Figure 1. Geometrical description of a typical offset strip fin
core.
solutions. Over eight decades of work has been associated
with offset strip fin heat exchangers, and Manglik and
Bergles [12] have compiled an extensive bibliography.
Though experimental investigations predominate in the
literature [5, 12], analytical modeling and numerical solu-
tions have also been carried out. However, most theoreti-
cal solutions suffer from an oversimplification of the
flow-channel geometry. Except for Patankar and Prakash
[13], Suzuki et al. [14], and Xi et al. [10], all others have
considered zero fin thickness. Furthermore, stable laminar
wakes have been assumed, which is contrary to the results
of flow visualization studies; a transition from steady lami-
nar flow to an oscillating or vortex-shedding flow occurs at
higher flow rates [15-17]. The flow is generally character-
ized by a progression of laminar, second laminar (transi-
tional, or vortex-shedding, or oscillating flow), and turbu-
lent flow regimes [17]. Joshi and Webb [16] attempted to
incorporate these observations and geometrical parame-
ters of the offset strip fin flow channel into an analytical
model. Although a fully analytical model describes the
laminar flow region, a semiempirical approach is adopted
for the turbulent flow predictions.
Despite this broad investigative effort, reliable predic-
tion of heat transfer and pressure drop in offset strip fin
heat exchangers remains a difficult, restrictive, and often
uncertain process. The analytical models are either very
cumbersome or oversimplified. Most of the available em-
pirical correlations tend to inadequately describe the
trends in a larger database; the deficiencies of prevailing
correlations are discussed at length in the ensuing section.
Given the importance and wide range of applications of
offset strip fin heat exchangers, reliable prediction of heat
transfer coefficients and friction factors is necessary. This
is addressed in the present paper, and improved, more
generalized correlations for f and j are presented. These
are based on a reexamination of the available data in the
literature, identification of the effects of geometrical fea-
tures of offset strip fins and the associated enhancement
mechanism, and correlation of the appropriate asymptotic
behavior of the data. Finally, predictive equations are
devised that represent the data continuously from laminar
to turbulent flow.
THERMAL-HYDRAULIC PERFORMANCE
Many different correlations for heat transfer and pressure
drop in offset strip fin heat exchangers have been reported
in the literature. These are chronologically listed in Table
1, and typical comparisons between some of them are
graphed in Figs. 2 and 3. Manson [18] appears to have
made the first attempt at developing predictive equations.
However, the database he employed consists of dissimilar
geometries: scaled-up and actual offset strip fins, louvered
fins, and finned flat tubes. Kays [22] made one of the first
attempts at analytical modeling of the heat transfer and
friction loss in offset strip fins and proposed a modified
laminar boundary layer solution that includes the form-
drag contribution of the blunt fin edges. The often cited
Wieting [23] correlations are power law curve fits through
data for 22 geometries [Eqs. (6)-(9), Table 1] for laminar
or turbulent flows. For predicting f and j in the transition
region, extrapolating the equations up to their respective
intersection point is suggested. This, however, tends to
misrepresent the transition region as seen from Figs. 2
and 3. Also, there appears to be some discrepancy in the
hydraulic diameter definition, and it is not clear whether
all the data were referenced to one consistent definition.
On the basis of previously reported flow visualization
studies [15, 30, 31] and their own experiments, Joshi and
Webb [16] attempted to identify the transition from lami-
nar flow. As the flow rate increases, oscillating velocities
develop in the wakes, leading to vortex shedding with
further increase in Re; this acts as free-stream turbulence
for the downstream fins, thereby increasing the heat and
momentum transfer. The onset of oscillating flow and the
consequent change in wake structure were found to corre-
spond approximately to the departure from the laminar
region log-linear behavior of f and j. It was observed that
the velocity profile in the wake was affected by the fin
spacing s, thickness t, and length I. From the data on 21
offset strip fin cores given by Ix)ndon and Shah [25],
Walters [26], and Kays and London [4], it was determined
that the transition point can be predicted by the correla-
tion for Re* given in Eq. (14) (see Table 1).
Furthermore, Joshi and Webb [16] developed elaborate
analytical models to predict f and j. They incorporate the
heat transfer from the fin ends, the form drag due to the
finite fin thickness, and heat transfer and friction loss
from the parting plates. An attempt was also made to
model the effects of fin burrs and roughness with a
semiempirical approach. However, these models are quite
cumbersome, and in cognizance of the need for an easy-
to-use correlation, Joshi and Webb [16] reevaluated the
empirical equations of Wieting [23]. Adjusting the database
of 21 geometries [4, 25, 26] to their hydraulic diameter
definition (Table 1) and choosing the laminar and turbu-
lent flow limits as Re < Re* and Re > (Re*+ 1000),
respectively, they presented Eqs. (10) and (12) to predict j
and Eqs. (11) and (13) to predict f (see Table 1). Their
predictions are compared with typical data in Figs. 2
and 3.
Correlations for Offset Strip Fin Surface 173
Table 1. Chronological Listing of Heat Transfer and Friction Factor Correlations for Offset Strip Fin Cores
Investigator(s) Correlation Database / Remarks
1. Manson [18] (0.6( l /Dh)°SRe °'5, l /D h < 3.5 ( la) Norris and Spofford [19], three
J = ~ 0.321 Re °5, l /D a > 3.5 ( lb) four°ffSetscaled-upStrip fin cores;C°res; LondonJ°yner [20],and
Ferguson [21], one louvered fin
For Re < 3500: core and one finned fiat tube
( l l .8( l /D h) Re °'67, I /D h < 3.5 (2a) core.
f = ~ 3.371 Re °67, l /D h > 3.5 (2b)
For Re > 3500:
0.38(1/D h) Re 0"24, l /D h < 3.5 (3a)
f = 0.1086Re °24, I /D h > 3.5 (3b)
where the hydraulic diameter is defined by
D h = 2sh/(s + h).
2. Kays [22] j = 0.665 Ret -°'5 (4) Analytical model for purely laminar
f = 0.44(t/l) + 1.328 Re/- 0.5 (5) boundary layer flow over interrupted
plate surface.
3. Wieting [23]
4. Joshi and
Webb [16]
5. Mochizuki
et al. [27]
6. Dubrovsky
and Vasiliev [28]
Re _< 1000:
j = 0.483(l/Dh)-°162ot -0"184 Re 0.536 (6)
f = 7.661(l/Dh)-°3840~ -°'°92 Re 0.712 (7)
Re >_ 2000:
j = 0.242(l/Dh)-°322(t/Dh) °'°89 Re- 0.368 (8)
f= 1.136(l/Dh ) o.781(t/Dh) 0.534 Re-0.198 (9)
where D h = 2sh/(s q- h).
Re _< Re*:
j = 0.53 Re-°'5(l/Dh)-°~Sc~ -°'14 (10)
f = 8.12 Re- 0.74(l/Dh )- 0.41Og- 0.02 (1 1)
Re >_ Re* + 1000:
j = 0.21 Re-°4°(l/Oh)- °24( t /Oh )0"02 (12)
f = 1.12 Re- °36( l /Oh) - °65(t//Oh )0"17 (13)
where - 1
Re* =257(~) l23(~)°58Dh[ t+ 1.328(/~-h ) - °s ] (14)
and D h = 2(s - t)h/[(s + h) + th/l].
Re < 2000:
j = 1.37(1/D h) °25a-°184 Re -°'67 (15)
f = 5.55(l/Oh)-O.32ot 0.092 Re-0.67 (16)
Re > 2000:
j = 1.17(l/D h + 3.75)-l(t/Dh) °'°89 Re 0.36 (17)
f = 0.83(l/D h + 0.33)-°5(t/Dh) °'534 Re -°'2° (18)
where D h = 2sh/(s + h).
Re < Relim:
Nu = O.O00437(t/Dh)- 2"6(l/Oh)- 0.15 Re x (19)
where x = 2.2(t/Dh)°55(l/Dh) -°°2
Re > Reli m
Nu = O.O0723(t/D h) l6(l/Oh) °9REX (20)
where x = 1.2(t/Dh)°34(l/Oh) 0"15 and
Reli m = 3960(t/Dh)°25(l/Dh)°42; (21)
Re ___ Relim:
= 1.05(t/Dh) 1.OS(l/Dh) 0.217 Re x (22)
where x = - 0.277(t/D h) °285(1/Dh )°'°64.
Re > Relim:
= O.13l(t/Oh)-°'4a(l/Dh )-0"234 Re x (23)
where x = -O.O042(t /Dh)- l25( l /Oh) 0"39 and
Reli m = 448(t/D h) °653(l/Dh )0"09. (24)
Kays and London [24], 10 cores;
London and Shah [25], nine
cores; Waiters [26], two cores;
London and Ferguson [21],
one louvered fin core.
Kays and London [4], 18 cores;
London and Shah [25], one core;
Walters [26], two cores.
Experimental data for five scaled-up
offset strip fin cores [27].
Eleven cores in a double sandwich
arrangement but without the
splitter plate, which leaves a
" leakage" path between top and
bottom rows of strip fins. The
definition of D h is not explicitly
given. Also, the same Nu
equations are cited by Kalinin
et al. [29], and have been used
to correlate data for non rectangular
offset strip fin geometries.
174 R.M. Manglik and A. E. Bergles
j ,f
10
010
001
Surface: 1 /8 - 16.O0(D)
0 f. } ~ = 0.477, 6 = 0.1148, 3' = 0.106
• I
0 002 i , J ~ L L = ~ [ ~ , , ~ ,
150 103 104
Re
Figure 2. Comparison of f and j correlations with experi-
mental data of Kays and London [4] for the 1/8-15.61 offset
strip fin core. ( - - - ) Joshi and Webb [16]; ( ) Wieting [23];
( - - ) Mochizuki et al. [27].
Subsequently, two other sets of correlations appeared in
the literature. As seen in Table 1, the Mochizuki et al. [27]
correlations [Eqs. (15)-(18)] are once again a reworking of
the Wieting [23] equations, with the coefficients and expo-
nents modified to fit their own experimental data for five
scaled-up rectangular offset strip fin surfaces. Only fully
developed laminar or turbulent flow is considered, with an
abrupt change of flow regime at Re = 2000. Dubrovsky
and Vasiliev [28] presented experimental data for 11 dif-
ferent rectangular offset strip fin cores with a double-
sandwich construction. These are similar to surface 1/8-
20.06(D), for example, of Kays and London [4], except that
they do not have a splitter plate between the two tiers of
offset strip fins; instead, a "leakage" flow passage of three
to four times the fin thickness is provided. No specific
reasons were given for such a construction, and the effect
of the "leakage" path on the performance has not been
established. To predict Nusselt numbers and Darcy fric-
tion factors, Eqs. (19)-(24) were presented (Table 1) [28].
As in the case of Mochizuki et al. [27], only laminar and
turbulent flow conditions are considered. The limiting
Reynolds number for the two flow regimes are given by
Eqs. (21) and (24) for the Nusselt number and friction loss
predictions, respectively. Furthermore, the form of the
correlations is rather awkward, with the same geometrical
parameters appearing as coefficients and exponents of Re.
The Nu equations given here were also reported by Kalinin
j,f
10
010
001
0002
150
. . . . . i
Sur[ace: 1/8 - 15.61
• ,1, = 0.244, ~ = 0.032, 7 = 0.067
• J
- . % - -
' ' . . . . . J i i i t , i ~ i
10 3 10 '
Re
Figure 3. Comparison of f and j correlations with experi-
mental data of Kays and London [4] for the 1/8-16.00(D)
offset strip fin core. ( - - - ) Joshi and Webb [16]; ( - - ) Wiet-
ing [23]; (- -) Mochizuki et al. [27].
et al. [29] as being applicable to triangular offset strip fins,
and the origin of the equations is attributed to Voronin
and Dubrovsky [32].
As seen in Figs. 2 and 3, the existing correlations tend
to present a wide performance envelope, and they have
several shortcomings. In all cases, only established lami-
nar or turbulent flow is considered and the transition
region is ignored. This extends over a fairly large Re range
of 1000 in the case of Wieting [23] and Joshi and Webb
[16]. Mochizuki et al. [27] and Dubrovsky and Vasiliev [28]
completely ignore the transition region and consider an
abrupt change from laminar to turbulent flow; the evi-
dence in the data for actual cores [4, 25] is contrary to
this. Furthermore, most of the equations are a reworking
of the Wieting [23] expressions, with constants and expo-
nents changed to fit different data sets. Little attempt has
been made to consider a large database that would extend
their general validity. Also, the equations do not necessar-
ily relate the performance to all the pertinent geometrical
attributes of the offset strip fin surface.
NEW DESIGN CORRELATIONS
Analysis of Experimental Data
To understand the effects of various geometrical at-
tributes of offset strip fins, experimental data for airflows
Correlations for Offset Strip Fin Surface 175
with heat transfer for 18 different cores I given by Kays
and London [4], Waiters [26], and London and Shah [25]
have been examined. These surfaces are listed in Table 2
along with their pertinent geometrical parameters. As
Joshi and Webb [16] have established, for the case of
uniform offset of half-fin spacing, the dimensionless pa-
rameters a = s /h , 6 = t / l , and 3" = t / s describe the off-
set strip fin geometry. Their influence has also been
documented in other experiments [33, 34] and numerical
studies [13, 14, 35]. Furthermore, the listed hydraulic
diameter in Table 2 is given by the following definition:
4A~ 4shl
D h (27)
Al l 2(sl + hl + th) + ts
As discussed previously [12], there appears to be no con-
sensus in the literature over definition of the hydraulic (or
equivalent) diameter in terms of the geometrical dimen-
sions of offset strip fins. The usual definition employed is
either 4Ac/P or 4Ac/ (A / I ) , where Ac, P, and A have
been evaluated differently by various investigators; at least
three different expressions for D h can be identified in the
literature [12]. In the present case, on a unit fin channel
basis, the free flow or channel flow area is taken as
Ac = sh, and the mass flux per channel is given by G =
rh/Nsh. In evaluating the heat transfer area A, the blunt
fin edges, both vertical and lateral, have been included as
well as the channel surface area. This is consistent with
the conventions of London and Shah [25] and Joshi and
Webb [16].
In Fig. 4, the f and j data for two pairs of surfaces,
each with the same value of 6 but different aspect ratio
a, are presented. The influence of a is clearly discernible;
the effect is almost the same in both laminar and turbu-
lent flows, with higher f and j for smaller values of a.
The fin thickness introduces a form drag and affects the
heat transfer. Also, as the boundary layer grows over the
fin surface, it is abruptly disrupted at the end of the fin
offset length I. Essentially, for the flow over short lengths
of fins of finite thickness, there is an outward displace-
ment near the leading edge, .followed by a local accelera-
tion near the trailing edge and the eventual dissipation of
the boundary layer in the fin wakes. As documented by Xi
et al. [10] and Lee and Kwon [9], these effects are shown
schematically in Fig. 5; the fin thickness and offset length
tend to have a competing influence on the flow field.
Moreover, thicker fins have larger form drag and heat
transfer contributions from blunt fin edges, whereas with
slender and longer fins, f and j are