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Rheology, flow behaviour and heat transfer of ice slurries:
a review of the state of the art
V. Ayel, O. Lottin*, H. Peerhossaini
Laboratoire de Thermocinetique, CNRS UMR 6607, Ecole Polytechnique de lUniversite de Nantes, BP 50609, 44306 Nantes, France
Received 25 October 2001; received in revised form 23 February 2002; accepted 26 February 2002
Abstract
This paper reviews recent studies on rheology, flow behaviour and heat transfer of two-phase aqueous secondary
refrigerants (ice slurries). The difficulties in measuring their rheological properties for which standard rheometers prove
to be poorly adapted are analysed. Special attention is paid to vane-in-cup rheometers, which can make it possible to
determine the yield stress. Pressure losses in cylindrical tubes have been measured by many authors. Even if the results
generally agree with two-phase flow theory, divergences in sensitivity to the solid fraction can be observed. The strati-
fication observed by some authors for small-Reynolds-number flows and its effects on the pressure drop are addressed.
In a last part, information concerning numerical values of the heat transfer coefficient of ice slurries are summarized.
Heat transfer coefficients depend on many parameters, but are largely influenced by the flow regime. A geometry of
heat exchanger is then proposed, which has already been effective for single-phase flows, and which may enhance heat
transfer in ice slurry flows.# 2002 Elsevier Science Ltd and IIR. All rights reserved.
Keywords: Two-phase secondary refrigerant; Ice slurry; Rheology; Heat transfer; Pressure loss; Survey
Rhe ologie, pertes de charge et transferts de chaleur des coulis
de glace : une revue de le tat de lart
Re sume
Cet article passe en revue des etudes recentes concernant la rheologie, le comportement des ecoulements et le transfert
thermique des frigoporteurs diphasiques aqueux (coulis de glace). Les difficultes de mesure des proprietes rheologiques,
pour lesquelles des rheome`tres courants save`rent mal adaptes, sont analysees. Une attention particulie`re est portee sur lesrheome`tres du type vane-in-cup qui permettent de determiner la contrainte seuil dun materiau. Les pertes de charge
lineaires dans des canalisations cylindriques ont ete mesurees par de nombreux auteurs. Meme si les resultats sont
generalement conformes a` la theorie des ecoulements diphasiques, on peut observer des divergences quant a` la sensibilite a`
la concentration en glace. La stratification, observee par quelques auteurs pour des ecoulements a` faible nombre de Rey-
nolds, et ses effets sur la chute de pression sont etudies. Dans une dernie`re partie, les valeurs numeriques du coefficient de
transfert thermique des coulis de glace sont recapitulees. Les coefficients de transfert thermique dependent de nombreux
0140-7007/03/$20.00 # 2002 Elsevier Science Ltd and IIR. All rights reserved.
P I I : S 0 1 4 0 - 7 0 0 7 ( 0 2 ) 0 0 0 1 6 - 6
International Journal of Refrigeration 26 (2003) 95107
www.elsevier.com/locate/ijrefrig
* Corresponding author. Tel.: +33-240-683-153; fax: +33-240-683-141.
E-mail address: [email protected] (O. Lottin).
http://www.elsevier.com/locate/ijrefrig/a4.3dmailto:[email protected]:[email protected]://www.elsevier.com/locate/ijrefrig/a4.3d -
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parame`tres, mais sont fortement influences par le regime decoulement. Nous proposons enfin un type dechangeur de
chaleur, dont lefficacitea deja` eteremarquee pour des ecoulements monophasiques, et il pourrait saverer tout a` fait adapte
a` des ecoulements de coulis de glace. # 2002 Elsevier Science Ltd and IIR. All rights reserved.
Mots cles : Caloporteur diphasique ; Coulis ; Rhe ologie ; Transfert de chaleur ; Chute de pression ; Base de donne es ; Enquete
1. Introduction
Cold distribution by means of secondary refrigerant is
an alternative solution to direct expansion systems,
which require large quantities of refrigerant. Ice slurries
exploit the latent heat of ice and are much more efficient
heat carriers than single-phase fluids; their high apparent
heat capacity results in lower mass flow rates and tem-
perature changes. Also, they are suitable for cold storage.
However, because of the presence of solid particles within
the carrying fluid, the flow of slurries is highly constrained.
It is thus necessary to determine the rheological nature of
these fluids for a better flow control in distribution plants.
At the present state of the art, the data and opinions ofdifferent authors are often divergent, so that reliable
conclusions on the rheology and flow behaviour of ice
slurries are difficult to draw. However, the technological
advantages of ice slurries and their potential economic
impact are great enough to warrant a critical review of
past work, the suggestion of new research areas, and the
search for new design geometries.
This paper first focuses on the rheology of the liquid
ice mixtures and assesses recent studies on ice slurries.
In the second part we address the flow and pressure
losses of slurries in cylindrical pipes by examining some
previous work on the subject. Then, the stratification
phenomenon observed by some authors for small-Rey-
nolds-number flows and its effects on pressure drops are
treated. In the last part we study the numerical values
and the evolutions of the heat transfer coefficients in
rectilinear cylindrical type geometries and we propose a
promising design geometry that enhances transport
phenomena between the ice slurries and a solid wall.
2. Rheological behaviour of ice slurries
Liquidsolid mixtures are often considered as non-
Newtonian; Table 1 gives examples of non-Newtonian
models that can be used to characterise slurries. Itshould be noted that some of these models could be
satisfactory on a restricted range of shear rates but
completely inappropriate on wider ranges.
Common to most of these models is a yield stress
below which no flow is observed. The value of the yield
stress depends strongly on the solid particle fraction:
Nguyen and Boger [1] suppose that the yield stress is
linked to the interaction and attraction among particles,
giving rise to structures larger than the primary crystals;
the yield stress then represents the breaking limit of these
structures. Similarly, Barnes [2] suggests that the yield
stress is a consequence of microstructural reorganization
Nomenclature
C thermal conductivity (W m1 K)
d particle diameter (m)
D tube diameter (m)
f friction factor
Fr Froude number
Gz Graetz number
h heat transfer coefficient (W m2 K)
H height of the vane (m)
He Hedstrom number
K constant of proportionalityL tube length (m)
n power index
Nu Nusselt number
Pr Prandtl number
Re Reynolds number
T torque (N m)
V velocity (m s1)
xs mass fraction of solids (wt.%)
:
shear stress (s1)
P pressure drop (Pa)
l specific heat (J kg1 K1)
viscosity (Pa s)
density (kg m3)
shear rate (Pa)
0 yield stress (Pa)
s volume fraction of solids (%)
Subscripts
ai antifreeze (initial value)b Bingham
c Casson
D-B DittusBolter
exp experimental
m average (for solidliquid mixture)
MAX maximum
s solid
w water-antifreeze (fluid)
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in the stagnant mixture into a structure allowing flows.
In spite of this, the real definition of the yield stress isstill a subject of discussion. For instance, the Bingham
model can lead to an overestimation of the yield stress if
not properly used. One sees in Fig. 1 that if a nonlinear
shear stress and shear rate behaviour is represented by a
linear function f :
, then the apparent yield stress is
higher than its real value. The yield stress cannot be con-
sidered as a fundamental property of the material as long
as its value depends on the model or on the viscometer [1].
3. Measurement of the rheological properties of ice slurries
Rheological measurements with ice slurries require
significant care, making experimentation difficult. There
are many reasons for these difficulties; some specific to
ice slurries and some linked to the general features of
liquidsolid mixtures:
frictions generated by the apparatus during
rheological measurement will induce warming of
the sample and modification of its ice content;
the low viscosity of the carrying fluid requires
small gap to allow accurate measurements; on
the other hand, the relatively large ice crystals
(from 10 mm to a few hundred mm) require muchlarger gap;
the stratification of solid particles, according to
their shape and size, does not permit to keep
samples homogeneous;
end effects (stresses on surfaces that ideally should
not be considered in measurement) are not easy to
take into account in stress-field calculations;
glides between solid particles and wall, or even
within the tested material, may significantly
complicate measurements.
The carrying fluid in ice slurries can generally beconsidered as Newtonian, as can slurries themselves if
the ice mass fraction remains low. Authors are in good
agreement that the ice mass fraction limit separating
Newtonian and non-Newtonian behaviours is between 6
and 15% (Table 2). Christensen and Kauffeld [5] propose
a correlation for apparent viscosity:
w 1 2:5s 10:052s 0:00273exp16:6s
1
Many authors attempted to reduce or suppress stratifi-
cation in ice slurries during rheological measurements:
pumping systems can remove particles from the upper
parts of the apparatus to inject them in the lower parts;
helical grooves may prevent stratification in rotating
viscometers at higher shear rates. Klein et al. [9] studied
the stratification rate of particles according to the height
of the vessel, considering the intermediate level at which
the particle concentration would remain, for some time,
constant and equal to the initial concentration.
Other authors tried to minimize the end effects. In
rotating viscometers for instance, the higher part of the
bob is not immersed in the sample while the lower part
can be dug so as to insert an air bubble during
measurement, which minimises stress transfer to thebob. This method is effective with viscoplastic fluids that
tend to maintain the bubble but will be delicate to
implement with ice slurries [10].
Barnes [11] studied glide in two-phase liquidsolid
mixtures inside viscometers. He explains that a narrow
layer of the carrying fluid free of particles (depletion
zone), establishes between the wall and the fluid. This
depletion zone acts as a lubricant. According to Barnes,
glides can explain the thixotropy phenomenon men-
tioned by some authors. Nguyen and Boger [12] report
that glide effects are all the more significant when the
solid fraction is high or the particles are flocculated. On
Table 1
Rheological non-Newtonian models that can be used for ice
slurries.
Tableau 1Mode`les rheologiques non-newtoniens pouvant etre utilises pour
les coulis de glace
Models Equations
Ostwald K0: n0
:5 0
Bingham 0 B:
> 0:
0 < 0Herschel-Buckley 0 K
0n0
> 0:
0 < 0
Casson 1=20 c
1=2h i2
> 0
:
0 < 0
Fig. 1. Comparison of yield stress values given by a linear
(Bingham) and a non-linear model.
Fig. 1. Comparaison de la contrainte de cisaillement entre un
mode`le lineaire (Bingham) et un mode`le non lineaire.
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the other hand, glide effects can be reduced by using a
larger gap between the rotating and fixed part of the
viscometer or a larger tube diameter. Barnes [13] esti-
mates that the gap must be at least 20 times greater than
the average particle diameter, provided that this dia-
meter stays below 0.25 mm. This ratio increases for
higher particle diameters.
Nguyen and Boger [12] compared the efficiency of
viscometers used with liquidsolid mixtures. The cone
plate and plateplate viscometers are proscribed because
the distance between the cone or the upper plate and the
lower plate is smaller than the particle size. Further-
more, the liquid will be expelled from the lower plate.
According to Yoshimura and Prudhomme [14], who
carried out experiments in order to compare 3 types ofviscometers (parallel plate, bob-in-cup and vane-in-cup
viscometers), the parallel plate viscometers are the least
appropriate apparatus for the determination of the yield
stress. The capillary viscometer is efficient in the sense that
it simulates the flow of the mixture in a pipe. It is also less
affected by the melting of the ice during the process (the
fluid crosses the tube, unceasingly regenerated at the entry
of the viscometer), but the measurements are distorted on
the one hand by the end effects (pressure drops in the input
and output of the tube) and on the other by the glide
effects, which cause the particles to concentrate in the
center of the tube [12].
Vane-in-cup viscometers are sometimes used for
rheological measurements with liquid-solid mixtures.
Their external cylinders are similar to those of bob-and-
cup viscometers but the bob is replaced by vanes (Fig. 2),
generally four of them. According to Barnes [13], vane-
in-cup viscometers have several advantages:
since the inner cylinder is replaced by some uni-
formly moving fluid, glide effects are minimised;
due to their reduced thickness, the vanes create
little disturbance within the sample;
the gap can be sufficiently wide compared to the
size of the particles.
However, vane-in-cup viscometers are well adaptedfor high-viscosity mixtures, which ice slurries are not
when the ice mass fraction is low. Furthermore, one can
often use them only to measure the yield stress; while
the vane rotates at constant speed, one observes a max-
imum value of the torque that corresponds to the tran-
sition between elastic and plastic behaviour. The
relation between the maximum torque and the yield
stress is:
TMAX D 3
2
H
D
1
m
!0 2
Table 2
Rheological behaviour of ice slurries
Tableau 2Comportements rheologiques des coulis de glace
Authors Descriptions of the
slurries
Viscosimeters Results
Bel and Lallemand [3] xs eau.
Jensen et al. [6] xs
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where H is the immersed height and D the external dia-
meter of the vane; m is a parameter characterising the
end effects, equal to 3 or 6 depending on whether or not
the vane is completely immersed in the sample. The
main design parameters for accurate measurements have
been summarised by Nguyen and Boger [15]. Barois et
al. [16] added a vibrating membrane inside a vane-in-cup viscometer to reduce stratification.
4. Distance flow and pressure drop in cylindrical ducts
According to Darby [17], the flow of suspensions can
be classified in three categories:
in homogeneous flows, the particle fraction is
large and the average particle diameter is much
smaller than the characteristic length of the
pipe; the dispersion can then be considered as auniform single-phase fluid.
In heterogeneous flows, the average particle size
is no longer negligible compared to the charac-
teristic length of the pipe, and the particle
fraction is lower or the density of the solid
phase is very different from that of the carrying
fluid.
In saltated flows, two phases of different den-
sities are clearly separated and the particles
accumulate at the bottom or at the top of the
pipe, thus constituting a bed of suspensions.
Generally, practical flows are often a combination of
homogeneous and heterogeneous flows.
Quemada [18] listed the parameters that differentiate
these three kinds of flows:
the geometric characteristics of the suspensions:
the particle drag coefficient depends on a Rey-
nolds number whose characteristic length may
include one or more ratios describing particleshape and orientation in the flow;
the concentration of particles: interactions
increase with solid fraction, having an effect
starting from 2 to 3% [19];
the density: adding solid particles changes the
density of the mixture, the Reynolds number
and the stratification speed. It has a dominating
influence on the saltation of the particles.
The model suggested by Darby [17] indicates that in a
constant-velocity flow, the pressure drops are always
higher in a two-phase mixture than in the carrying fluidonly. In Fig. 3, the dashed line represents the evolution
of the linear pressure drop according to the velocity in a
pipe filled with the carrying fluid only. There is a cri-
tical deposit rate Vm2 that ensures minimum displace-
ment of the solid particles and can be interpreted as the
transition between saltated and heterogeneous flows.
This transition velocity was observed with most of the
slurries and corresponds to a minimum of the pressure
drop. It may be useful to approach this velocity, but at a
velocity higher than the critical deposit rate, in order to
minimise the pressure drop and to avoid stratification.
Concerning the ice slurries flows, it is noted (Table 3)
that in many cases [3,4,6,2027], the evolution of the
pressure drop corresponds well to the general behaviour
Fig. 2. Schematic diagram of a vane-in-cup viscometer.
Fig. 2. Diagramme dun viscosime`tre de type vane-in-cup.
Fig. 3. Pressure gradient plotted versus mean velocity for the
various flow regimes (xs represents ice fraction) [17].
Fig. 3. Pertes de charge en fonction de la vitesse moyenne pour
differents regimes decoulement xs
represente la fraction de
glace) [17].
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described by Darby [17]. Jensen et al. [6] and Bel and
Lallemand [3] observed no change in the pressure drop
with changing ice mass fraction provided it remained
lower than 1015%. For Winters and Kooy [27], the
pressure drop measured with the slurry is even veryclose to that obtained with the carrying fluid for ice
mass fraction not exceeding 22%. Snoek and Joanis [21]
made the assumption that the ice slurry friction factor
could be determined from the knowledge of the water-
only and waterglycol (liquid only) friction factors, and
developed a correlation for this. On the other hand, in
some works, like these of Liu et al. [28], Knodel and
France [30] and Knodel et al. [31], the pressure drop
decreases with an increase in the ice fraction, which
seems to be contrary to general studies on two-phase
flows. Knodel et al. explain this observation by a
decrease in the flow turbulence caused by interactions
between the fluid and the particles. According to them,
there is a critical ice fraction beyond which the pressure
drop remains constant (30% in this case). Knodel et al.
[31] found that for small tubes, Reynolds numbers ran-
ging from 38,000 to 74,000 and when xs was above 4%,
they could write:
f
0:18Re0:2 0:946 3
Knodel and France [30] observed that when the pipe
diameters are low, the number of interactions betweenthe wall and particles increases, which tends to intensify
friction and to decrease the damping of turbulence. Liu
et al. [28] confirm this hypothesis and argue that the
solid particles bring a coherent structure to the fluid,
thus decreasing the energy dissipated by viscous fric-
tions. They propose a correlation:
P 15:135V1:931m 0:02227s 4
where Vm is the mean velocity and s is the solid
volume fraction.
5. Flow stratification
The forces acting on a single particle in a flow are
(Fig. 4): the gravitational force, which is toward the
bottom, the buoyancy force, and the drag force of thefluid on the particle; the latter is a function of the velo-
city difference between the solid and liquid phases. Its
direction is mainly that of the flow, with an added
component in the direction opposed to that of the par-
ticle sedimentation (if a movement of sedimentation is
induced). The drag force can slow down or even prevent
saltation. Some other forces acting on the particles that
are more complex to determine arise from the inter-
action among particles and between the particles and
the walls. Their direction is random, but it tends to slow
down the saltation rate, and due to the non-uniformity
of the movements it acts on the whole field of saltation.
The stratification velocity thus depends on several
parameters:
The particle size and shape: these parameters act
primarily on the drag coefficient of the fluid on
the ice crystals. The drag force can be reduced to
its simpler expression for rigid spherical particles,
Table 3 (continued)
Authors Description of the slurries Geometries Comments
Knodel et al. [31] s
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but their influence is more complex when their
shape is far from spherical. The effect of the par-
ticle shape on the drag coefficient results in a
modification of the critical velocity for saltation.
Generally, this factor is taken into account in cal-
culations by coefficients of nonsphericity.
The particle weight: the average rate of saltationis proportional to the relative density of the
crystals and of the carrying fluid.
The solid concentration: interactions between
particles and the particles wakes slow down the
saltation rate. On the other hand, a high mass
fraction of ice may induce flocculation of the
crystals. Agglomerations of particles will trap
fluid, and the whole will move at sedimentation
velocities higher than those of the single parti-
cles. These formations are controlled by the
nature of the flow. As long as the relative influ-
ence of flocculation and particle interaction willbe unknown, stratification of ice crystals will
remain difficult to describe.
To approach an optimal flow by minimizing the
pressure drop, one has to be as close as possible to the
laminated flow mode (see Fig. 3). However, this presents
the risk that the flow will be in a laminated or stationary
bed mode, which would increase solid friction between
the particles and the walls. According to Takahashi et
al. [25] and Kawashima et al. [33], pressure drops in ice
slurry flows are higher than those in pure liquid at low
speeds, because ice particles accumulate at the top of the
horizontal pipe, sometimes even forming solid blocks.
These phenomena disappear at higher speeds (Vm> 1.6
m s1). For Inaba [22], the effects of the drag force
depend on the particle size: the smaller particles accu-
mulate at the top of the tube while the larger ones, on
which the drag is more significant, remain below. Snoek
et al. [21] observed that below the velocity Vm2, solid
friction is more significant, and the bypass section of the
carrying fluid (with Vfluid> Vice) is reduced. Pressure
drops thus increase even at reduced speeds. In the same
way, Winters and Kooy [27] studied Vm2, which seems
to be dependent on xs (for xs=7.5%, Vm2=0.12 m s1,
while for xs=12%, Vm2=0.18 m s
1). They alsoobserved contacts between the ice particles and the wall
for flow rates lower than 0.3 m s1.
Sasaki et al. [34] studied the particle-fluid relative
velocity, which tends to increase with increasing average
flow speed, thus preventing particle settlement.
6. Cooling coil performance
Table 4 gathers the informations available on the heat
transfer coefficient h or the Nusselt number Nu
[3,5,6,23,29,31,3540]. As a general rule, the majority of
observations show that h or Nu increase with the flow
rate (velocity, mass flow rate or Reynolds). Only Knodel
et al. [31] an Snoek and Bellamy [35] observed that Nu
decreases with increasing xs. Meewisse and Ferreira [23]
propose a correlation for the calculation of the Nusselt
number in laminar flow of ice slurries in circular tubes:
Nu 38:3Gz0:15x0:52s 5
where Gz RePrD4z
is the Graetz number, and z is the
axial distance along the tube. Re and Pr are respectively
the Reynolds and the Prandtl numbers, calculated with
the average properties of the ice slurry. The viscosity
was evaluated with the correlation (1) of Christensen
and Kauffeld [5]. This equation is valid for 35%:
Nu
Nuw 1 0:103xs 2:003Re
0:192 30xs30 x
0:339 Re10000
s 12
where Re and Nu are calculated with the properties of
the ice slurry, and Nuw is calculated with the properties
of the carrier fluid, using the average velocity. Eq. (1)
was used to evaluate the viscosity. This model estimates
the measured values within 35%, and 75% of the
measurements are estimated within 30%. The validity
of the correlation is limited to tubes with an inner dia-
meter between 18 and 25 mm. Christensen and Kauffeld
[5] suggest that the melting of ice crystals close to the wallreduces the temperature gradient through the boundary
layer, which can explain the increase in the heat transfer
coefficient.
Ben Lakhdar et al. [39] and Inaba [22] studied the
evolution of the Nusselt number with the length covered
in the heat exchanger. The value of Nu decreases slowly
with the progression of the slurry in the heat exchanger,
and tends towards the values of Nu corresponding to
the single phase flow. Kawanami et al. [40] studied the
evolution of the heat transfer coefficient h in a heat
exchanger, formed by a tube bended at 180 in a vertical
plane. At the concave wall, h increases with the velocity
of the flow. For velocities higher than 0.4 m s1, h
decreases according to the angle of the bend, whereas
for velocities close to 0.1 m s1, h decreases then stays
constant. At the convex wall, h decreases according to
the angle of the bend, but for velocities close to 0.1 m
s1, it tends to be in general greater than that for the
other velocity conditions at the area from 0 to about
120. The friction of ice crystals against the wall, caused
by their stratification, could explain these phenomena.
The increase in the velocity of ice slurry flow causes an
increase in the accumulation of the ice particles in the heat
transfer area of the concave wall, as well as the decrease
of the depletion zone thickness, owing to the mixing
effects based on both the centrifugal and the inertial
forces.
Flow geometries that can combine the low-pressurelosses of laminar flows and efficient mixing would be
particularly adapted to flows of ice slurry. An example
of such geometries consists of a series of bent tubes with
planes of curvature at a 90 angle with respect to the
previous tube, thus creating alternating Dean flows
whose chaotic characteristics can enhance mixing and
heat transfer (Fig. 5). The counterrotating secondary
flows called Dean roll-cells appear in curved duct due
to the centrifugal force, that pushes the fluid particles
against the concave wall. If the curvature plane of the
curved ducts maintains the same orientation (as in a
helical coil), the flow has the same structure at the
Table 4 (continued)
Authors Description of the
slurries
Geometries Comments
(ethanol) Di=38 mm
L=0.5 m
h (xs=0%)=500 W/m2C, h (xs=35%)=
2000 W/m2 K.
Ben Lakhdar et al. [39] xs
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entrance and at the exit of the coil, i.e. a regular Dean
flow. On the other hand, if each bend is turned 90
compared to the preceding one, the Dean roll-cells
formed in an elbow are broken by the subsequent one,
which imposes a different orientation on them. In a coil
composed of a series of elbows with alternating curva-
ture planes, the fluid particles follow chaotic trajec-
tories, even for small Reynolds numbers, allowing better
homogenisation of the particle distribution and tem-
peratures within the fluid. This phenomenon increases
heat transfer considerably, provided that the Reynolds
numbers stay low [41]. It is then possible to improve the
efficiency of heat exchangers used with high viscosity
fluids without increasing the velocity and the pressure
losses.
In a numerical study, Mokrani et al [42] used a reduced
model to compute the flow in a helical and a chaotic coil,
and observed the distribution at the exit plane of 40,000
passive tracer injected at a point in the input section. Fig. 6
shows that for a tracer injection at the centre of the input
section and a Reynolds number of 40, the mixing is far
more homogeneous in the chaotic coil than in the helical
one, and this only after 10 bends. At the output of the
chaotic coil the particles are in close to total apparent
disorder, whatever the injection position of the particles.
On the other hand, in the helical coil the particles follow
the trajectories of the regular Dean roll-cells, which do
not evolve in the flow direction.
Mokrani et al. [43] also found experimentally that at
very low Reynolds numbers (Re=63) the chaotic coil
has a heat transfer efficiency 28% greater than the heli-
cal coil. This type of coil could probably be adapted to
the flows of ice slurries, either to allow efficient mixingof ice particles all along the distributing pipes, or to
optimize heat transfer in some heat exchangers. Fig. 7
shows that the temperature profile at the outlet of the
chaotic coil, for a Reynolds number of 63, is flat and does
not exceed a temperature difference of 3 K, while it reaches
12 K for the helical coil under the same conditions.
7. Conclusions
The rheological study of ice slurries suffers from a ser-
ious handicap, since no current apparatus has really
Fig. 6. Images of the injected tracer after passing through dif-
ferent numbers of bends, for both helical and chaotic configur-
ations [42].
Fig. 6. Images du filet de traceur deforme par lecoulement en
fonction du nombre de coudes et de la position dinjection, pour la
configuration helicodale et la configuration chaotique [42].
Fig. 7. Temperature profile at the exit of the two heat exchan-
gers for two measurements, and for Reynolds number 63 [43].
Fig. 7. Profils de temperature a` la sortie des deux e changeurs de
chaleur pour deux mesures et pour un nombre de Reynolds de 63
[43].
Fig. 5. Dean-roll-cells in a curved duct.
Fig. 5. Cellules de Dean dans une conduite incurvee.
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proved satisfactory: vane-in-cup rheometers, which seem
in general well adapted to liquidsolid two-phase systems,
do not allow precise measurement of any rheological
characteristics except the yield stress. These difficulties are
due to the low viscosity of the carrying fluid, to the size of
the crystals and to the stratification problem (which
could be perhaps be solved by small recirculationpumps). The capillary rheometer can be used to measure
the linear pressure drops in a cylindrical pipe according
to the average speed of the mixture and to the ice frac-
tion, as many authors did, but viscosity measurements
will be disturbed by glide effects and end effects. In any
case, opinions seem to converge on the proposition that
the pressure drop increases with average speed and tends
to approach that of the carrying fluid. On the other hand,
different authors do not agree on the behaviour of ice
slurries with ice fraction, probably because of different
flow reorganisation patterns in different regimes. Studies
of the stratification regimes confirm Darbys [17] theoryof a critical deposit rate that increases as the solid
fraction increases.
Although the experimental conditions are different,
the heat transfer coefficients seem to follow the same
behaviour overall, from the point of view of the orders
of magnitude of the numerical values as well as their
evolutions according to various parameters.
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