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Rheological properties of coarse food suspensionsin tube flow at high temperatures
Krittalak Chakrabandhu 1, Rakesh K. Singh *
Department of Food Science, Purdue University, W. Lafayette, IN 47907-1160, USA
Received 3 April 2001; received in revised form 27 January 2004; accepted 24 February 2004
Abstract
The effects of particle concentration and carrier fluid temperature on rheological behavior of model food suspensions consisting
of 1.5% CMC solution and green peas (1530% v/v) were investigated using a tube viscometer. The flow behavior of the suspensionswas represented by the power law model. The suspension consistency coefficient (m) increased with particle concentration and
decreased with temperature, whereas the opposite trends were observed for the suspension flow behavior index ( n). Among various
theoretical, semi-empirical, and empirical equations tested for suspension apparent viscosity (l) estimation, the third order
expansion of Einstein equation, which was derived via the hydrodynamic approach, provided the best estimates for l. Of equations
tested for m estimation, those in which n was included offered better estimates of experimental values, with an empirical equation
obtained based on the Einstein equation and the incorporation of n term providing the best m estimation. These findings suggest
that, for concentrated coarse suspensions subjected to conditions presented here, the dependence between m and n is of importance
and should be considered in order to achieve a better m estimation. Besides, better representations for power law parameters of such
suspensions may be obtained based on a theoretical expression derived for l via the hydrodynamic approach. The study presented
here provides a much-needed insight toward the flow behavior of concentrated coarse food suspensions at high temperature,
information of which is vital for various food processes.
2004 Elsevier Ltd. All rights reserved.
Keywords: Non-Newtonian fluids; Rheological properties; Coarse suspension; Particulate foods
1. Introduction
Designing an aseptic process requires information
about flow properties of the foods. Flow properties have
significant effects on the residence time distribution and
heat transfer of the particulate food system as reported
by several researchers (Awuah, Ramaswamy, Simpson,
& Smith, 1996; Ramaswamy, Awuah, & Simpson, 1996;
Sandeep & Zuritz, 1994). A number of studies have been
done on rheological behavior of fluid foods and manyare summarized by Holdsworth (1971). However, only a
few studies on rheological behavior of coarse food sus-
pensions can be found in the literature, especially with
the carrier fluids that exhibit non-Newtonian behavior
(Bhamidipati & Singh, 1990; Martinez-Padilla, Cornejo-
Romero, Cruz-Cruz, Jaquez-Huacuja, & Barbosa-Ca-
novas, 1999; Pordesimo, Zuritz, & Sharma, 1994).
Due to the larger particle size, only few types of
viscometers can be used in characterizing the flow
behavior of coarse suspensions. These include tube
viscometers (Bhamidipati & Singh, 1990), wide-gap
parallel plate viscometer (Pordesimo et al., 1994), wide-
gap rotational viscometer (Martinez-Padilla et al.,1999). The above-mentioned equipments are although
functional, difficulties still exist especially in the studies
for dense suspensions. Some of the difficulties could be
caused by the interference to the equipment parts by the
large particles as reported by Martinez-Padilla et al.
(1999), centrifugal effects in the parallel plate viscometer
as pointed out by Pordesimo et al. (1994), or simply
large amount of materials and floor space required to
run the tests using the tube viscometer. This leads to the
scarcity of the knowledge on the flow behavior of coarse
food suspensions. More insight on the flow behavior of
Journal of Food Engineering 66 (2005) 117128
www.elsevier.com/locate/jfoodeng
* Corresponding author. Address: Department of Food Science and
Technology, University of Georgia, Food Science Building, Athens
30602, USA. Tel.: +1-706-542-2286; fax: +1-706-542-1050.
E-mail address: [email protected] (R.K. Singh).1 Current address: Death Receptor Laboratory, Institute of Signal-
ing, Developmental Biology and Cancer Research, CNRS UMR 6543,
33 Ave. de Valombrose 06189, Nice, France.
0260-8774/$ - see front matter 2004 Elsevier Ltd. All rights reserved.
doi:10.1016/j.jfoodeng.2004.02.039
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coarse food suspensions particularly in the conditionsapplicable to aseptic processing is clearly desirable. The
objectives of this study were (1) to characterize the flow
behavior of model food suspensions consisting of non-
Newtonian carrier fluid and high concentration of large
particulates at high temperatures, (2) to investigate the
effect of particle concentration and temperature on flow
behavior of non-Newtonian coarse suspensions, and (3)
to investigate the applicability of several mathematical
expressions in explaining the effect of particle concen-
tration on the flow behavior of coarse suspensions.
2. Materials and methods
2.1. Food system
Green peas were used as model particulate phase
because of their commercial availability and their
applications in real food in the market. Frozen green
peas were purchased from Purdue University food store.
Green peas were thawed and drained prior to each
experimental run.
An aqueous solution (1.5% w/v) of sodium carboxy-
methylcellulose (CMC) (TIC Gum, Inc., Belcamp, MD)
was selected as the carrier fluid. The CMC solution wasprepared by slowly adding the desired amount of CMC
powder into a mixing tank filled with water continu-
ously agitated by a mechanical mixer. The mixture was
agitated for approximately 45 min then left overnight
(1215 h) for the CMC to dissolve. Prior to the experi-
mental run, the CMC solution was mixed with green
peas to attain the specified particle volume fractions
(1530%v/v). Due to the delicate texture of green peas,
the CMC-pea suspension was made in several small
batches of 0.0379 m3 to achieve the desired particle
concontration. The suspension was mixed manually to
ensure the uniform distribution of green peas in the
suspension and then delivered into the pump feeder
during the experimental run. The physical properties of
the food materials are summarized in Table 1.
2.2. Experimental setup
The rheological characterization of the fluid food,
with or without particulates in aseptic processing con-
ditions was performed using an in-line tube viscometer.
The schematic diagram of the experimental setup is
shown in Fig. 1. The system consisted of a 150 l feed
tank, a moving pocket type pump (Moyno Product
Progressive cavity pump, Robbins and Myers, Inc.,
Springfield, OH), a helical double tube heat exchanger
(46.3 m long, 0.032 m I.D.) as a heater, a helical doubletube heat exchanger (33.5 m long, 0.032 m I.D.) as a
cooler (Stork, Amsterdam, Netherlands), an electro-
magnetic flow meter (Promag 33, Endress and Hauser
Inc. Greenwood, IN), an insulated straight stainless steel
tube (0.022 m I.D.), a differential pressure transducer
(Rosemount Model 3051 Smart Pressure Transmitter,
Rosemount Inc., Eden Prairie, MN), resistance tem-
perature devices (RTDs), and a programmable logic
controller (PLC, 5-15, Allen-Bradley Co., Inc. Milwau-
kee, WI) for control and data acquisition. The tube
viscometer (2.89 m long) is located in the straight tube
Nomenclature
D tube diameter, m
L length, m
Le entrance length, m
m fluid consistency coefficient, Pa sn
m suspension consistency coefficient, Pa sn
n fluid flow behavior index
n suspension flow behavior index
P pressure, Pa
Q volumetric flow rate, m3/s
Qws volumetric flow rate without slip, m3/s
Qm measured volumetric flow rate, m3/s
r tube radius, m
Re Reynolds number
T temperature, C
Greek charactersb slip coefficient, m Pa1 s1
/ particle volume fraction
/m maximum particle volume fraction
_c shear rate, s1
_cw wall shear rate, s1
l suspension apparent viscosity, Pa s
lf fluid apparent viscosity, Pa s
lr relative viscosity (l=lf)
s shear stress, Pa
sw wall shear stress, Pa
Table 1Physical properties of model food system
Property Value
Green peas
Average diameter (m) 0.0084 0.0025
Density (kg/m3) 1026 9.770
CMC solution (1.5% w/v)
Density (kg/m3) 1022 5.000
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section of the system. The entrance length (Le) of 3.44 m
(Le > 100 I.D.) was used to avoid the entrance effect.The entrance length was verified against the equation
given by Kays (1966).
Le
D
Re
20 1
2.3. Experimental run
Water was pumped through the system until the
system reached the desired temperature. Then the test
food suspension was delivered to the positive displace-
ment pump. Once the flow and temperature stabilized,
the data of flow rate and pressure drop were collected
with the data acquisition system. The suspension was
not reused after heating due to the change in rheological
properties of CMC solution being heated at high tem-perature. The experimental parameters are summarized
in Table 2.
2.4. Wall shear stress and wall shear rate calculations for
tube viscometry
The relationship between shear rate and shear stress
was obtained from the measurement of pressure gradi-
ent and volumetric flow rate based on the following
assumptions: (a) steady flow, (b) time independent fluid
properties, (c) fluid velocity has no radial or tangential
components, (d) no slip condition at pipe wall, (e)incompressible fluid, and (f) isothermal flow. Wall shear
stress was calculated from:
sw rDP
2L2
Shear rate was calculated using RabinowitschMooney
equation
_cw 3Q
pr3 sw
dQ=pr3
dsw3
The derivative term in Eq. (3) was obtained by taking
the derivative of a function from curve fitting the plot ofQ
pr3vs. sw.
When a tube viscometer is used to study the flow
behavior of dense coarse suspension, wall effects would
be present. The slip at wall occurs when fluid, having
lower viscosity than the bulk suspension, forms a thin
lubricating layer at the wall of the tube. Since the Ra-
binowitsch-Mooney equation was derived based on the
assumption of no slip at wall, the effect of the slippagemust be corrected in order to use the equation to obtain
the true shear rate. The classical method for slip cor-
rection can be found in the literature (Mooney, 1931;
Jastrzebski, 1967; Steffe, 1996). The correction is done
by introducing a term to account for the added flow due
to wall slippage to the overall flow rate. This results in
the following equation:
Qm
swpr3
Qws
swpr3b
r4
Generally, the effective slip coefficient, b, is evaluated
using tubes of different radii. However, to determine theslip coefficient by varying the tube radius would require
large amount of food materials in this study. Recog-
nizing the similar effect of varying tube radius and
varying particle concentration on the wall shear stress,
an alternative procedure based on the utilization of
variable particle concentration was used to determine
the slip coefficient. The procedure has been described by
Chakrabandhu (2000). The slip coefficient was then used
for flow rate correction. The corrected volumetric flow
rate was subsequently used to calculate the true wall
shear rate.
Table 2
Experimental parameters for study of rheological properties of coarse
food suspensions
Parameter Value
Carrier fluid temperature (C) 85, 110, 135
Particle concentration (% v/v) 0, 15, 20, 25, 30
Volumetric flow rate (m3/s) 1.261043.15 104
Fig. 1. Schematic diagram of the experimental setup for the study of coarse suspension flow behavior at high temperature.
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2.5. Flow behavior characterization of coarse food
suspensions
Once the true shear rate was calculated, flow behavior
parameters of the suspension were computed. As several
studies have reported that the flow behavior of suspen-
sions follows power law pattern, the power law para-
meters of the coarse suspension were investigated. The
suspension consistency coefficient (m) and flow behav-
ior index (n) were estimated by fitting the experimental
data in the power law model (Eq. (5)) using linear
regression (SAS, 1989).
ln s ln m n ln _c 5
The suspension apparent viscosity (l) was then calcu-
lated from
l m _cn1 6
An analysis of variance (ANOVA) was performed for
the effects of particle concentration and suspensiontemperature on the consistency coefficient and flow
behavior index of suspensions.
2.6. Mathematical representation of apparent viscosity for
coarse suspensions
Selected theoretical expressions from the literature
developed from various approaches, i.e. hydrodynamic
approach (Einstein, 1905; Ting & Luebbers, 1957), en-
ergy approach (Frankel & Acrivos, 1967) as well as
semi-empirical (Mooney, 1951; Thomas, 1965) expres-
sions were considered for the prediction of the apparentviscosity of suspensions that contain high concentra-
tions of coarse particulates. A statistical test (v2-test)
was performed to determine the goodness of fit of the
mathematical expressions to the experimental results.
The v2 value is expressed as:
v2 Xni1
Ymeasured Ypredicted2
Ypredicted
!7
The null hypothesis of no significant differences between
the predicted and experimental results is rejected if the
calculated v2 value is larger than the tabulated critical
value (c) depending on the confidence level (a) and de-gree of freedom (df). The expressions tested are listed
below.
Einsteins equation
lr l
lf 1 2:5/ 8
Second-order expanded Einsteins equation
lr 1 2:5/ 10:05/2 9
The second-order coefficient of 10.05 arrived after con-
sidering the hydrodynamic interaction of spheres and
the effect of double formation due to collisions (Thomas,
1965).Third-order expanded Einsteins equation
lr 1 2:5/ 10:05/2 a/3 10
Thomass equation
lr 1 2:5/ 10:05/2 aeb/ 11
Instead of expanding the power series to the third order,
Thomas proposed that the fourth term which represents
the particle interaction to be an exponential term as
suggested by Eyring, Henderson, Stover, and Eyring
(1964). The empirical constants, a and b, in Eq. (11)
were given by Thomas as 0.00273 and 16.6, respectively.
Mooneys equation:
log lr 2:5/
1 k/12
where k is an empirically determined parameter sug-
gested by Mooney to be in the range of 1.351.91. Sincek is a parameter related to the packing geometry, several
numerical values that represent theoretical packing
geometries along with some that have been presented in
the literature were used to investigate the fit of the
Mooney equation to the experimental data from this
study. The values and their significance are summarized
in Table 3. The value of k was also empirically deter-
mined to obtain the best fit to the experimental data.
FrankelAcrivoss equation
lr b/=/m
1=3
1 /=/m
1=3" # 13The FrankelAcrivos equation was derived based on the
assumption that the particle shell is spherical and b takes
the value of 9/8. Instead, if a cubical particle shell was
assumed, b would take the value of 3p=16. In the veri-fication of their equation, Frankel and Acrivos used the
/m value of 0.625 which was obtained by Thomas (1965)
from available data in the literature. In this study, the
values of b and /m were varied (Table 4). The /m value
was also empirically determined to obtain the best fit to
the experimental data.
Table 3
Values of k tested for best fit of Mooneys equation to experimental
data
k Value Significance
1.350 Lower bound for k suggested by Mooney
1.910 Upper bound for k suggested by Mooney
0.340 Maximum volume fraction for completely tetrahe-
dral packing
0.524 Maximum volume fraction for completely cubical
packing
0.625 Maximum volume fraction used by Thomas (1965)
and Frankel and Acrivos (1967)
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TingLuebbers equation
lr /m
/m /14
In the same manner as the tests for other expressions
mentioned above, the values of /m in the TingLueb-
bers equation was also varied (0.34 and 0.524) and an
empirical value of/m was also determined to obtain the
best fit for the equation.
2.7. Mathematical representation of power law para-
meters for coarse suspensions
Compared to the expressions for apparent viscosity
of suspension, smaller number of mathematical expres-
sions relating the power law parameters to the solid
fraction exist. In this study, the following equations
proposed by Jarzebski (1981) were tested for the fit to
experimental results.
Modified FrankelAcrivoss equation
m
m
9
8
/=/m1=3
1 /=/m1=3
" #n15
m
m
3p
16
/=/m1=3
1 /=/m1=3
" #n16
Modified Mooneys equation:
lnm
m
2:5/
1 k/
n17
Empirical equations of simple forms listed in Table 5
were also fitted to the experimental data to describe the
dependence of power law parameters on the particle
volume fraction in the conditions covered in this study.
Due to the fact that the consistency coefficient and the
flow behavior index together represent the flow curve of
suspensions, it was considered that a better prediction of
consistency coefficient could be obtained if the descrip-
tive equation also contained the flow behavior index
term or vice versa. Also, most of the previously de-
scribed mathematical expressions, which have been
shown in the literature to describe well the l and m
values, contain the particle fraction terms in the form of
the volume fraction-to-maximum volume fraction ratio
(/=/m) or those similar to the what given in the Einsteinequation. Therefore the following equations were also
investigated:
m
m a
/
/m
bn
n
c18
m
m
a1 2:5/b n
n
c
19
3. Results and discussion
3.1. Effects of particle concentration and temperature on
power law parameters of coarse suspensions
From the known value of slip velocity, the corrected
volumetric flow rate was computed and used in calcu-
lation of the true shear rate according to the Rabi-
nowitschMooneys equation. The flow curves were
plotted for suspensions at 85, 110, and 135 C in Figs. 2
4. The suspensions exhibited power law behavior. Flow
behavior parameters of the suspensions were determined
according to the power law model. An analysis of var-
iance (ANOVA) was performed for the effects of particle
concentration and temperature on the consistency
coefficient (m) and flow behavior index (n) of suspen-
sions. The power law parameters of the suspensions are
summarized in Table 6.
Table 5
List of empirical equations of simple forms used to describe thedependence of power law parameters on the particle volume fraction
Power law
parameter
described
Basis of empirical equation
Volume fraction to
maximum volume
fraction ratio
Einstein equation
Consistency
coefficient
m
m a /
/m
bm
m a1 2:5/
b
m
m a /
/m
bnc m
m a1 2:5/
bnc
Flow Behavior
Index
n
n a /
/m
bn
n a1 2:5/
b
a, b and c are empirical constants.
Fig. 2. Shear stressshear rate relationships for suspensions at 85 C
and various particle concentrations.
Table 4
Constants tested for best fit of FrankelAcrivos equation to experi-
mental data
Parameter Values
B 9/8, 3p=16/m 0.340, 0.524, 0.625
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Particle concentration and temperature showed sig-
nificant effects on the consistency coefficient and the flow
behavior index (P < 0:0001). In general, the consistencycoefficient increased with particle concentration and
decreased with temperature as shown in Fig. 5. For all
experimental temperatures, as the particle concentration
was increased from 0% to 15%, the consistency coeffi-
cient increased significantly (a 0:05). However, thesuspension at 85 C, which possessed highest carrier
fluid viscosity, exhibited a much higher rate of increasein consistency coefficient than what was observed for the
suspensions at higher temperatures. As the particle
concentration level increased from 15% to 20% and
25%, although slight increase in consistency coefficient
was observed for suspensions at 110 and 135 C, no
significant change in the consistency coefficient was
observed at 95% confidence level for all experimental
temperatures. As the particle concentration level in-
creased from 25% to 30%, the consistency coefficient
increased significantly (a 0:05) for suspensions at85 C and 110 C whereas no significant change in the
consistency coefficient was observed at 135 C. For all
particle concentrations, suspensions at 85 C showedsignificantly higher consistency coefficient than those at
higher temperatures. When comparing the suspensions
at 110 C and 135 C at the same level of particle con-
centration, however, the difference between the suspen-
Fig. 5. Effects of particle concentration and temperature on the con-
sistency coefficient of coarse suspension.
Table 6
Power law parameters for CMC solution with and without particulates
Temperature (C) Particle concentration (%v/v) Consistency coefficient, m (Pasn) Flow behavior index, n Shear rate, _c (1/s)
85 0 5.1 0.47a 0.510 017a 159374
15 26 4.1b 0.30 0.016b 44.6125
20 23 4.0b 0.35 0.038b 35.7115
25 26 1.7b
0.32 0.023c
69.124830 39 8.7c 0.25 0.050d 33.0118
110 0 1.6 0.21d 0.58 0.020e 115372
15 2.1 0.62e 0.58 0.082e 73.4205
20 1.8 0.09e 0.62 0.008e 114190
25 3.0 0.35e 0.56 0.019f 71.8126
30 7.9 0.88f 0.36 0.017g 151247
135 0 0.35 0.085g 0.75 0.047h 125209
15 1.4 0.11e;h 0.55 0.017e;i 108266
20 2.0 0.71e;h 0.51 0.081e;i 99.1263
25 1.5 0.29h 0.59 0.056f;i 82.8158
30 1.5 0.10h 0.56 0.014i 155229
* Values having same superscripts (ai) are not significantly different at a 0:05.
Fig. 4. Shear stressshear rate relationships for suspensions at 135 C
and various particle concentrations.
Fig. 3. Shear stressshear rate relationships for suspensions at 110 C
and various particle concentrations.
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sions at these temperatures was not as discernable. Al-
though the suspensions at 110 C generally had higher
consistency coefficient than those at 135 C, as can be
seen at 25% and 30% particle concentration levels
(P < 0:01), the difference was insignificant at the particleconcentration levels of 15% and 20%.
The flow behavior indices indicate shear-thinning
behavior for all suspensions (n < 1). The effects of par-ticle concentration and temperature on flow behavior
index of coarse suspensions were in opposite trends of
the effects on the consistency coefficients. That is, in
general, the flow behavior index decreased with an in-
crease in particle concentration and increased with
temperature as shown in Fig. 6. As for the effect of
temperature, even though the difference between the
flow behavior indices of the suspensions at 110 and 135
C was not evident at the particle concentration levels of
2025%, the difference at 30% particle concentration
level was very noticeable. As the particle concentration
was increased from 0% to 15% the flow behavior indexdecreased significantly (a 0:05) for suspensions at 85C and 135 C. At 110 C, however, the flow behavior
index did not exhibit a significant difference as the par-
ticle concentration increased from 0% to 15%. When the
particle concentration was increased from 15% to 20%,
no significant changes in the flow behavior index was
observed at all temperature tested. As the particle con-
centration was increased from 20% to 25% and 30%, an
evidently decreasing trend (a 0:05) could be observedfor suspensions at 85 C and 110 C. The suspensions at
135 C, however, did not exhibit any significant changes
as the particle concentration increased.
It should be noted that for mixtures containing high
concentration of coarse particulates (i.e., 1530%), as
the viscosity of the carrier fluid increased, the influence
of particle concentration was more pronounced. Also, as
the particle concentration increased, the influence of the
carrier fluid viscosity was more pronounced. This indi-
cates a significant interaction (P < 0:005) between par-
ticle concentration and temperature (which reflects the
effect of carrier fluid viscosity) on the power law
parameters of coarse suspensions. Also, the effect of the
interaction between these variables was more observable
on the consistency coefficient than on the flow behavior
index.
The effect of temperature on the consistency coeffi-
cient of CMC solution containing no particulates (m)
can described satisfactorily by an Arrhenius-type equa-
tion
m AeEa=RT R2 0:986 20
where the pre-exponential constant (A) and the activa-
tion energy are 0.0000014 mPa sn and 66 kJ/(gmol),
respectively.
For the flow behavior index (n) of the CMC solution,
the effect of temperature, can be described well by an
exponential equation,
n 0:2138 exp0:0092T R2 0:996 21
Exponential function have been used successfully to
express the effect of temperature on CMC solution in the
temperature range below 70 C (Bhamidipati & Singh,
1990).
3.2. Mathematical expressions for apparent viscosity of
coarse suspensions
Variations of Einstein, Mooney, FrankelAcrivos,
and TingLuebber expressions, as well as the expression
presented by Thomas (1965) were tested for the good-
ness of fit to the experimental data. The results aresummarized in Table 7. It was found that most expres-
sions tested adequately represented the apparent vis-
cosity for the entire range of particle fraction covered in
this study. The original Einstein equation (Eq. (8)) ex-
plained the suspensions apparent viscosity quite well for
the entire range of/. As a matter of fact, the Einsteins
equation was the best in explaining the suspension
apparent viscosity at the higher temperature range (110
and 135 C), i.e., for the lower levels of fluid apparent
viscosity. Expanding the Einsteins equation to second-
order (Eq. (9)) improved the prediction of suspension
apparent viscosity at the lower temperature level (85
C), i.e., higher fluid apparent viscosity. However, it didnot appear to improve the prediction for the entire range
of particle fraction. When the Einsteins equation was
expanded to the third-order, with the second order
coefficient of 10.05 and the best-fit third-order coefficient
(a 20:84), i.e.,
lr 1 2:5/ 10:05/2 20:84/3 22
the prediction for the entire range of lr improved
markedly when compared to the prediction by the ori-
ginal Einsteins equation. Thomas (1965) noted that
the fourth term in the expanded Einsteins equationFig. 6. Effects of particle concentration and temperature on the flow
behavior index of coarse suspension.
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Table 7
Summary of goodness of fit test values (v2) for apparent viscosity expressions of coarse suspensions
Equation Variation v2 value
0:15 < / < 0:30 (df 37, c 24.08) 0:15 < / < 0:20 (df17, c 8.68) 0:25