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Sidorenko, I., & Rhodes, M. J. (2004) Influence of pressure on fluidization properties. Powder Technology, 141, 137-154.
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www.elsevier.com/locate/powtec
Powder Technology 141 (2004) 137–154
Influence of pressure on fluidization properties
Igor Sidorenko, Martin J. Rhodes*
Cooperative Research Centre for Clean Power from Lignite, Department of Chemical Engineering, Monash University, P.O. Box 36, Clayton,
Victoria 3800, Australia
Received 27 August 2003; received in revised form 12 December 2003; accepted 25 February 2004
Available online 13 April 2004
Abstract
An experimental study of the influence of pressure on fluidization phenomena was carried out in a bubbling fluidized bed over the range of
operating absolute pressures 101–2100 kPa with Geldart A and B bed materials in an apparatus 15 cm in diameter. Bed voidage data was
gathered using electrical capacitance tomography (ECT) and the resulting time series were analysed to give average bed voidage, average
absolute deviation, average cycle frequency and Kolmogorov entropy. Bed collapse tests were also performed to establish the influence of
operating pressure on dense phase voidage. For theGeldart B powderUmf was found to decrease slightly with pressure whilst voidage atUmf was
unaffected and no change in behavior from Geldart B to A was observed. Analysis of the ECT results for the Geldart B powder showed no
influence of pressure on cycle frequency and average absolute deviation, but an increase in mean bed voidage with pressure. For the Geldart A
powder, no influence of pressure on Umf, Umb and emf was observed, though emb was found to increase slightly with pressure. Analysis of the
ECT results for the Geldart A powder revealed a decrease in average bed voidage, cycle frequency and average absolute deviation with pressure.
The trend in Kolmogorov entropy within increasing pressure was not entirely revealed over the range of velocities used, but results suggest a
decrease.
D 2004 Elsevier B.V. All rights reserved.
Keywords: Fluidization; Pressure effect; Electrical capacitance tomography
1. Introduction tion velocity is not a quantity with a precise significance for
Fluidized bed technology originated as the Winkler pro-
cess for lignite gasification developed in the 1920s and the
fluidization technique as it is known now was born from the
successful development of the fluidized bed catalytic crack-
ing process in the early 1940s. It has been known for some
time that the use of higher operating pressures increases the
rate of processes in fluidized beds and improves fluidization
quality [1]. Although some data on the effect of pressure on
the behavior of fluidized beds have been obtained during the
past 50 years and several comprehensive review papers have
been published [2–5], areas remain where further experi-
mental work and analysis would be warranted.
In industrial practice fluidized bed reactors are mostly
operated at superficial gas velocities well above the minimum
fluidization velocities and, therefore, the minimum fluidiza-
0032-5910/$ - see front matter D 2004 Elsevier B.V. All rights reserved.
doi:10.1016/j.powtec.2004.02.019
* Corresponding author. Tel.: +61-3-9905-3445; fax: +61-3-9905-
5686.
E-mail address: [email protected] (M.J. Rhodes).
industrial applications, however discussion on accurate pre-
diction of the minimum fluidization velocity still seems to
remain of much scientific interest. The effect of pressure on
the minimum fluidization velocity has been studied by many
researchers [6–19]. The common finding is that the effect of
pressure on the minimum fluidization velocity depends on
particle size. The results of the experiments show a decrease
in the minimum fluidization velocity with increasing pressure
for particles larger than 100 Am (Geldart B and D materials);
however, for fine Geldart A particles the minimum fluidiza-
tion velocity is unaffected by pressure.
Under ideal experimental conditions, Abrahamsen and
Geldart [20] expected a very weak effect of pressure on the
minimum bubbling velocity. However, this effect is still
relatively unknown and findings in the literature are some-
what controversial. Sobreiro and Monteiro [18] found that
the influence of pressure on the minimum bubbling velocity
could be very different for different bed materials, but failed
to explain their results. According to Jacob and Weimer
[21], it has generally been found that with increasing
pressure for systems of Geldart A powders the minimum
Fig. 1. Pressurized fluidized bed apparatus used in this study.
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154138
bubbling velocity increases, however, the extent of the
pressure effect and the reason for it is uncertain.
There are also conflicting reports on the effect of increas-
ing pressure on the bed voidage at minimum fluidization (emf)
and minimum bubbling (emb) conditions. According to Bin
[22], for industrial design purposes the assumption that emf
does not change with pressure and that emf can be taken as that
experimentally determined at atmospheric conditions is jus-
tified for the majority of solids. Several researchers reported
that the voidage at minimum fluidization emf is essentially
independent of pressure [11,18,19]. Yang et al. [23]suggested
that the variation of the voidage at incipient fluidization
caused by increase in pressure is negligible for Geldart B
and D materials and expected an appreciable change with
pressure for Geldart A. Weimer and Quarderer [24] observed
only very small increase in bed voidage at minimum fluid-
ization with increase in pressure for Geldart A materials and
no change in voidage for Geldart B solids. Contrary to that,
Olowson and Almstedt [16] observed a slight increase of the
voidage at minimum fluidization with pressure for Geldart D
particles and did not notice any dependence of the voidage emf
on pressure for Geldart B particles.
Rowe [25] presented some of his calculations which
showed no measurable change in predicted minimum bub-
bling voidage, however, these predictions are not in agree-
ment with experimental findings of other researchers
[11,26,27] who generally observed an increase in minimum
bubbling voidage with pressure.
When fluidized beds operate in the bubbling regime, they
consist of the dense (emulsion) phase and bubbles. The
dense phase voidage is an important parameter in determin-
ing the fluidized bed performance because it is widely
believed that it has a direct influence on chemical reactions
in the fluidized bed. It affects the degree of gas–solid
contact and heat and mass transfer. It is also believed that
in Geldart A powders the equilibrium size of the bubbles
may be controlled by the dense phase voidage [28]. The
dense phase voidage is generally taken as being equal to its
value at the minimum fluidization point for Geldart B and D
materials, but can be higher for Geldart A powders [28,29].
A few methods have been used to measure the dense
phase voidage in bubbling fluidized beds. For Geldart A bed
materials the voidage can be measured by means of the bed
collapse technique. This method has a few variations but
generally it involves abruptly stopping the gas flow to a
vigorously bubbling fluidized bed and measuring the rate of
collapse of the bed surface (e.g. Refs. [30–32]).
Other techniques for measuring voidage in fluidized beds
involve the use of capacitance probes, optical fibres, X-ray
or g-ray attenuation and capacitance tomographic imaging
[29,33]. A non-invasive technique for fast measurement of
solids volume fraction in bubbling fluidized beds was
pioneered at Morgantown Energy Technology Centre
(METC) in the US and at the University of Manchester,
Institute of Science and Technology (UMIST) in the UK. By
the early 1990s both development groups had successfully
demonstrated the technique, which became known as the
electrical capacitance tomography (ECT).
In this work, the influence of pressure on fluidization
phenomena, such as minimum fluidization velocity, mini-
mum bubbling velocity, bed expansion and voidage was
studied; and a novel diagnostic technique suitable for online
monitoring of fluidized bed behavior was tested. Experi-
ments were conducted in a bubbling fluidized bed at
operating pressures up to 2100 kPa and ambient temperature
with Geldart A and B materials [34]. Pressure probe, visual
observation and the electrical capacitance tomography were
used for characterizing the fluidized bed behavior at elevat-
ed pressure. Although the ECT technique has been used in
fluidization research [35–37], it has not been previously
used to study the fluidized bed behavior in a pressurized
environment.
2. Experimental
2.1. Equipment
The process and instrumentation diagram of the pressur-
ized fluidized bed used in this study of pressure effects on
fluidization is given elsewhere [38]. The pressure vessel,
capable of operating at pressures up to 2600 kPa, was 2.38
m high and was equipped with five glass observation ports.
One of two 15-cm diameter plastic fluidized bed models
was inserted into the pressure vessel and used to study
physical behavior of gas-fluidized beds (Fig. 1). Both
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 139
fluidized bed columns were identical and made of clear
plastic; however the second column had a permanently
mounted capacitance sensor described below.
The bottom flange of the column was bolted to a carbon
steel plenum chamber and distributor assembly, and the top
flange was bolted to an expanded top freeboard for solids
disengagement. The plenum chamber and distributor as-
sembly were designed and manufactured according to
recommendations given by Svarovsky [39]. Two types of
distributor plates were specially made for the study. The
first distributor was made from a sintered bronze plate with
nominal pore size of 12 Am and the pressure drop through
the plate of 4.9 kPa at a superficial gas velocity of 0.5 m/s.
The second distributor was designed for pressure drop
experiments for Geldart A materials so that the pressure
drop was approximately 6.5 kPa at a superficial gas
velocity of 0.01 m/s in accordance with recommendations
by Svarovsky [39].
The assembled fluidized bed column was inserted into
the pressure vessel and positioned vertically. Provisions
were made in the design of the lid of the pressure vessel
for charging/discharging of solids and inserting bed differ-
ential pressure probe. Fluidizing gas for experiments was
supplied either from a building compressed air supply or
from dedicated nitrogen and compressed air cylinders and
metered by variable area flow meters. According to the
German Standard VDI/VDE 3513 Part 2, the rotameters of
the accuracy class 1.6 were properly compensated for
difference in gas properties at different operating pressures
and temperatures.
The operating pressure in the fluidized bed was set with a
backpressure control valve. The experimental facility was of
an open circuit type so the same gas was used for pressur-
izing the system and for fluidizing the solids. The apparatus
was pressurized to the desired operating pressure before the
fluidizing gas flow rate was adjusted to a desired value.
Bed pressure drop was measured using a simple differ-
ential pressure probe, having one leg at distributor level and
the other in the freeboard, and connected to a pressure
transducer and microprocessor-based data acquisition unit.
The electrical capacitance tomography (ECT) system
used in this work was a single plane system with driven
guard drive circuitry of PTL300 type manufactured by
Process Tomography.
The required electrode pattern for this work was designed
in accordance with PTL application note [40]. The maxi-
mum number of measurement electrodes (12) was used
together with driven guard electrodes. The sensor was
fabricated using standard printed circuit board design tech-
niques from flexible copper-coated plastic laminate that was
etched with the electrode pattern and wrapped tightly
around the fluidized bed plastic vessel. The sensor consisted
of 12 rectangular electrodes, 35 mm wide and 50 mm high.
The centers of the electrodes were located at the height of
250 mm above the distributor plate, or approximately at a
half of the static bed height used in the experiments.
In accordance with PTL recommendations, the measure-
ment and guard electrodes were connected to the data
acquisition module by 1.5-m-long screened coaxial cables,
terminated in miniature coaxial connectors. The capacitance
sensor had to be positioned inside the pressure vessel and,
since the data acquisition module was not designed for
operation at elevated pressure, it was located outside of the
pressure vessel. Therefore, it became necessary to direct 24
coaxial cables and an earth wire out of the pressure vessel
without gas leaks and pressure loss. The detail of how this
was achieved is given in Sidorenko [41].
Compressed air from a centralized building supply was
usually used for experiments when operating pressure did
not exceed 600 kPa. For other experiments that were usually
run at higher operating pressure, industrial grade nitrogen
supplied from a bank of 12 gas cylinders was used. Geldart
A FCC catalyst and Geldart B silica sand were used as bed
solids.
Geldart A FCC catalyst with the Sauter mean diameter of
77 Am contained 10.1% of fines less than 45 Am and had the
particle density of 1330 kg/m3. Particle size distributions
were measured using a Malvern Instruments Mastersizer
and particle density was determined by using a mercury
intrusion analysis. Seven kilograms of the powder were
used as the bed material for experiments to observe the
minimum fluidization and minimum bubbling conditions,
which gave a static bed height of 53.5 cm. For experiments
using the ECT system, 5 kg were used, and the bed height
was 44 cm. For bed collapse experiments, 6.56 kg of the
catalyst were used, which gave the bed height of 49.7 cm.
Geldart B silica sand of the narrow size distribution had
the Sauter mean diameter of 203 Am and the particle density
of 2650 kg/m3. Nine kilograms of the powder were used as
the bed material for experiments to observe the minimum
fluidization and minimum bubbling conditions, which gave
a static bed height of 40 cm. For experiments using the ECT
system, 10 kg were used, and the bed height was 42 cm.
The instruments downstream of the fluidized bed were
protected by a line filter capable of removing particles down
to 0.3 Am. Simple filter checks after each experiment
indicated that the fines carryover was negligible.
2.2. Minimum fluidization velocity
A single set of experiments was carried out in order to
determine the minimum fluidization velocity, minimum
bubbling velocity, bed expansion and voidage at minimum
fluidization and minimum bubbling conditions; and the
details of the experimental procedure are given here. Bed
pressure drop measurements were obtained for both increas-
ing and decreasing gas velocities. The minimum fluidization
velocity is taken as the velocity at the intersection point of
the line corresponding to the constant bed pressure drop in
the fluidized state and the extrapolated straight line of the
packed bed region. There is no agreed procedure for
determining the precise point of the minimum fluidization
I. Sidorenko, M.J. Rhodes / Powder T140
velocity and, usually, the two straight lines are obtained as
the gas flow rate is gradually reduced in increments from a
vigorously bubbling state. In this case, a slightly larger
value of the minimum fluidization velocity is obtained. That
makes sense for industrial applications as it provides a
maximum experimental value for the minimum fluidization
velocity and, therefore, the lowest limit for potential defluid-
ization of a process.
According to Svarovsky [39], better reproduction of
results can be obtained by allowing the bed to mix first
by bubbling freely before turning the gas flow rate down to
zero and then taking pressure drop measurements, while
increasing gradually the gas flow rate. However, various
researchers have described three different points represent-
ing the minimum fluidization velocity on the increasing gas
velocity curve for Geldart A materials, as reviewed by
Fletcher et al. [42].
A certain procedure was followed for preparing the bed
for the experiments. Prior to each experiment at ambient
conditions, the pressure vessel was open and the air supply
pressure was set to the gauge pressure of 100 kPa. The bed
was fluidized at superficial gas velocities well above the
onset of fluidization for at least 15 min, allowing bed solids
to fully mix. To achieve an initial packed bed of similar
structure in each experiment, the air supply was then slowly
turned off by closing the flow control valve.
In high-pressure experiments the same gas was used for
pressurizing the system and then for fluidizing the bed
material. Therefore, prior to each experiment, the back-
pressure controller was set to a pre-determined operating
pressure and the system was pressurized to that level first. At
the same time, the gas passed through the fluidized bed,
which was properly fluidized for much longer than at the
ambient conditions. Then the gas supply was slowly turned
off, allowing the bed to settle in the pressurized environment.
In actual experiments, measurements of the pressure drop
were taken for both increasing and decreasing gas velocities.
After each gas velocity change, the pressure in the system
was allowed to stabilize for at least 10 min and then pressure
drop measurements were recorded at a frequency of 1 Hz for
at least 3 min. For each experiment a straight line was drawn
from the origin through the series of bed pressure drop points
until it crossed the horizontal line corresponding to bed
weight per unit area (there was generally good agreement
between measured data and this horizontal line). The point of
intersection was taken as the value of minimum fluidization
velocity at a given experimental condition. Where measure-
ments showed a hysteresis effect between increasing and
decreasing gas velocities, both intersection points were
established as lower and upper values of the minimum
fluidization velocity at a given experimental condition. The
difference between the lower and upper values was generally
small, and for comparison between experiments at different
operating pressures the average of these two points was taken
as the minimum fluidization velocity. These experimental
curves are presented in Sidorenko [41].
2.3. Minimum bubbling velocity
The minimum bubbling velocity was measured by visual
observation of the point at which the first bubbles appeared
and by examination of the bed height variation with gas
velocity. Visual observation of the fluidized bed behavior
provides a common and simple but subjective way of
determining the minimum bubbling velocity. When the gas
flow is gradually increased, the gas velocity at which the first
distinct bubbles appear on the bed surface is recorded.
Alternatively, the gas velocity is noted at which bubbling
stops when the gas flow is decreased. According to Geldart
[28] and Svarovsky [39], the average of the two values
provides the minimum bubbling velocity, or more appropri-
ate values can be taken during decreasing gas flow. In this
work, measurements of the minimum bubbling velocity were
taken for both increasing and decreasing gas flow.
At each gas velocity the bed height was recorded and,
based on visual observation, general behavior of the bed
was noted. The first bubbles were not confused with the
small channels, which sometimes appeared and resembled
small volcanoes. Genuine bubbles usually appeared in
several places on the bed surface and were about 10 mm
in diameter; while the channels were smaller in diameter and
usually stayed in one place.
The minimum bubbling velocity was also determined
less subjectively as the velocity at which the maximum bed
height was observed [43].
2.4. Bubbling bed voidage
Experiments using the ECT equipment were carried out
at operating pressures ranging from 300 to 1900 kPa, using
Geldart A FCC catalyst as bed material, and ultra-pure
nitrogen and compressed air as fluidizing gases. Another
series of experiments was conducted at operating pressures
ranging from ambient to 1700 kPa, using Geldart B silica
sand as bed material, and industrial nitrogen and com-
pressed air as fluidizing gases.
Before commencing experiments, the ECT system was
calibrated by filling the sensor with the two reference
materials in turn and by measuring the inter-electrode
capacitances at the two extreme values of relative permit-
tivity (empty vessel and packed bed). The packed bed was
formed each time under relevant pressure and following the
same procedure (vigorous fluidization followed by gradual
defluidization).
Since some drift in the very sensitive electronic capac-
itance measuring circuitry was observed after a few hours of
fluidization, it became necessary to carry out such a cali-
bration twice a day and check its accuracy before and after
each experiment.
In actual experiments at pre-determined operating pres-
sure, the gas velocity was an experimental variable. After
each gas velocity change, the pressure in the system was
allowed to stabilize for at least 10 min. When both pressure
echnology 141 (2004) 137–154
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 141
and gas flow became stable, the tomographic data were
logged on an ECT dedicated computer. The ECT system
generated a cross-sectional image of the bed and showed the
solids volume fraction (the ratio of solids to gas) at sensor
level. Under each set of operating conditions, the behavior
of the bed was also characterized by visual inspection and
recording of bed height versus gas velocity.
2.5. Bed collapse method
Bed collapse experiments were carried out at room
temperature and the operating pressures ranging from atmo-
spheric to 1600 kPa, using 6.56 kg of Geldart A FCC
catalyst as bed material, and industrial nitrogen as fluidizing
gas. The experimental program was based on a ‘‘single-
vented’’ technique given by Geldart and Wong [44].
The bed collapse experiment was carried out as follows:
the gas flow rate was set at a predetermined level so that the
bed was bubbling, and the average bed height was recorded.
The gas supply was quickly isolated and the bed collapse
was recorded on a video camera at a rate of 25 frames per
second. The plenum chamber was not vented simultaneous-
ly. The combined internal volume of the chamber and the
pipeline downstream of the isolation valve was estimated to
be equal to 0.00115 m3. Since the bed height fluctuated due
to bubbling, five repeat tests were made and an average bed
height was taken. Similar tests were also carried out at
different predetermined gas flow rates.
Because of restrictions to our gas supply, we used initial
velocities in the range 0.054 m/s at atmospheric pressure to
0.008 m/s at 1600 kPa—somewhat below the 0.04 m/s
recommended by Geldart [45] and the higher values used by
Geldart (0.08 m/s in Geldart and Wong [44] and 0.1 m/s in
Geldart and Xie [30]).
3. Experimental results and discussion
3.1. Minimum fluidization velocity
Many researchers have previously studied the pressure
effect on the minimum fluidization velocity and found that
the minimum fluidization velocity is not affected by pressure
for fine Geldart A powders and decreases with pressure in-
crease for coarse materials. Numerous correlations for pre-
dicting the minimum fluidization velocity have been sugges-
ted with the most widely used correlation proposed by Wen
and Yu [46]. However, this popular correlation was based
only on data obtained at atmospheric pressure. Four similar
correlations based on experiments carried out at elevated pre-
ssures have also been proposed in the literature [6,9,15,17].
All the correlations are based on the Ergun [47] equation,
and are simplified by assuming certain fixed values for the
bed voidage at the minimum fluidization and constant
particle shape factor. Previously it was quite often found
that the absolute values of predictions based on the corre-
lations, available in the literature, were significantly in error
[12,14,16].
One of the better methods for prediction of the minimum
fluidization velocity, based on using the Ergun [47] equa-
tion, was suggested by Werther [48] and has been used in
the present work. Values of the minimum fluidization
velocity experimentally determined at ambient conditions
and the voidage at minimum fluidization, described in the
next section, were used to calculate a characteristic particle
diameter udp from the Ergun equation. Following this
method, which is described in Sidorenko and Rhodes [4],
the minimum fluidization velocity values at various operat-
ing pressures were calculated.
A comparison between the experimentally measured
values of the minimum fluidization velocity and the calcu-
lated values from the Ergun [47] equation and the available
correlations [6,9,15,17,46] is shown in Figs. 2 and 3.
For a Geldart A material, Fig. 2 shows that within the
studied pressure range the minimum fluidization velocity was
independent of the operating pressure, which is in line with
observations of other workers (e.g. Refs. [9,11,18,26,49,50]).
Many researchers (e.g. Refs. [6–19]) have observed the
decrease in the minimum fluidization velocity with increas-
ing pressure for Geldart B materials. Our results also show a
slight decrease in minimum fluidization velocity with in-
creasing pressure in the range up to 1600 kPa.
Depending on the physical properties of particles, the
correlations agree with the experimental results with vari-
able success. For the FCC catalyst, Fig. 2 shows that the
Ergun [47] equation and the correlations of Nakamura et al.
[15], and to some extent of Wen and Yu [46] predict the
minimum fluidization velocity values very well. However,
the correlations of Chitester et al. [9], and to larger extent of
Saxena and Vogel [17] and Borodulya et al. [6] overestimate
the minimum fluidization velocity values. Similar results
can be observed for the silica sand Geldart B material in Fig.
3, where only the Ergun [47] equation agrees well with the
experimental results and all the correlations more or less
overestimate the minimum fluidization velocity values.
3.2. Voidage at minimum fluidization conditions
Knowing the mass of the bed solids m and the bed cross-
sectional area A, the experimental values of the voidage at
minimum fluidization emf were determined, using measured
bed height Hmf values corresponding to the minimum
fluidization velocity at both increasing and decreasing gas
velocity. The average of the two values was used as a
parameter for comparison at various operating pressures.
It was experimentally found that the voidage at minimum
fluidization was essentially independent of pressure for:
� Geldart A FCC catalyst (emf = 0.42) in a pressure range
101–1100 kPa.� Geldart B silica sand (emf = 0.50) in a pressure range
101–1600 kPa.
Fig. 2. Variation of the minimum fluidization velocity with pressure for Geldart A FCC catalyst. Comparison of experimental values (clear squares) with
predictions from the Ergun equation [47,48] (line 4) and correlations of Borodulya et al. [6] (line 1); Chitester et al. [9] (line 3); Nakamura et al. [15] (line 5);
Saxena and Vogel [17] (line 2); and Wen and Yu [46] (line 6).
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154142
Other workers [11,18,19] also observed the indepen-
dence of the voidage at minimum fluidization on pressure.
Yang et al. [23] suggested, however, that the variation of the
voidage at minimum fluidization caused by a pressure
increase would be very small, if at all, for coarse materials
and substantial for Geldart A powders. That was not
observed in the present study. Weimer and Quarderer [24]
carried out their experiments at much higher pressures and
did not observe any voidage change for a Geldart B material
and noticed only very small increase in the voidage at
minimum fluidization for Geldart A materials.
Fig. 3. Variation of the minimum fluidization velocity with pressure for Gelda
predictions from the Ergun equation [47,48] (line 6) and correlations of Borodulya
Saxena and Vogel [17] (line 1); and Wen and Yu [46] (line 5).
3.3. Minimum bubbling velocity
The silica sand was found to exhibit Geldart B behavior,
with coincidence of minimum bubbling and minimum
fluidization velocities, for all pressures up to 1600 kPa.
This result is in agreement with the findings of King and
Harrison [11] at pressures up to 2500 kPa, but at odds with
the findings of Sobreiro and Monteiro [18] and Sciazko and
Bandrowski [51,52], who were able to establish separate
values for the minimum bubbling and minimum fluidization
velocities within the similar pressure range, as well as at
rt B silica sand. Comparison of experimental values (clear squares) with
et al. [6] (line 2); Chitester et al. [9] (line 3); Nakamura et al. [15] (line 4);
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 143
higher pressures up to 3500 kPa. These results are also
contrary to those of Varadi and Grace [53], obtained within
the pressure range from atmospheric to 2170 kPa. However,
it should be noted that the often-cited work of Varadi and
Grace [53] is only a preliminary study carried out in a two-
dimensional bed.
FCC catalyst showed a typical Geldart A behavior,
expanding without bubbling within a certain gas velocity
range at ambient conditions. At all the experimental con-
ditions the height of the homogeneously expanded bed of
the FCC catalyst was at least 0.6 m. In all cases the
minimum bubbling velocity values, determined visually,
coincided for both increasing and decreasing gas flow and
were equal to values, obtained from the maximum bed
height.
Only one correlation for determining the minimum
bubbling velocity has been proposed [20]. This equation
is not commonly used on its own as Abrahamsen and
Geldart [20] combined it with another correlation for the
minimum fluidization velocity [54] and proposed a more
popular relation:
Umb
Umf
¼2300q0:126
g l0:523expð0:716FÞd0:8p g0:934ðqp � qgÞ
0:934ð1Þ
Thus, Geldart A behavior corresponds to the velocity
ratio being more than unity. The minimum bubbling to
minimum fluidization velocity ratios calculated from the
experimental values of the minimum bubbling and mini-
mum fluidization velocities and compared to the predictions
of Eq. (1) are presented in Fig. 4.
As can be seen in Fig. 4, Eq. (1) predicts an increase
in the velocity ratio with increasing pressure but the
accuracy of prediction is quite low. It overestimates the
Fig. 4. Variation of the minimum bubbling to minimum fluidization velocity ratio w
(clear squares) with predictions from the Abrahamsen and Geldart [20] correlatio
experimental values for the FCC catalyst which show no
pressure effect on the velocity ratio over the range
considered.
Within the higher pressure range (2140 to 6900 kPa) and
in a smaller column (2.7 cm in diameter), Crowther and
Whitehead [55] fluidized 50 g of fine synclyst particles with
a high density gas (CF4) and found that the minimum
bubbling velocity was equal to 0.008 m/s at 2140 and
2820 kPa, and increased to 0.009 m/s at 4180 kPa and to
0.011 at 5540 kPa.
In another study within the pressure range similar to
present work, Richardson [56] fluidized Perspex particles at
pressures between atmospheric and 1400 kPa and reported a
‘‘slight increase’’ in the velocity ratio from 2.2 to 2.8.
However, when Richardson [56] fluidized similarly sized
phenolic resin particles, the velocity ratio trend was not
obvious.
It should be noted that, since both the minimum fluid-
ization and minimum bubbling velocities are very low, a
small variation of just 0.5 mm/s in either of them could
position the velocity ratio anywhere in the range between
two and three, as can be illustrated by substantial error bars
in Fig. 4.
3.4. Voidage at minimum bubbling conditions
Abrahamsen and Geldart [20] correlated the maximum
non-bubbling bed expansion ratio in the following way:
Hmb
Hmf
¼5:50q0:028
g l0:115expð0:158FÞd0:176p g0:205ðqp � qgÞ0:205
ð2Þ
According to this correlation, the maximum bed expan-
sion ratio should slightly increase with pressure. A compar-
ith pressure for Geldart A FCC catalyst. Comparison of experimental values
n.
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154144
ison between the maximum bed expansion ratio determined
experimentally and that predicted from Eq. (2) is shown in
Fig. 5.
As can be seen in Fig. 5, the effect of pressure on the
maximum bed expansion within the pressure range 101–
1100 kPa was found to be negligible for the Geldart A
material used in this work. Eq. (1) overestimates the
experimental values for the FCC catalyst. The experimental
results and predictions from Eq. (2), however, contradict the
experimental results presented by Piepers et al. [26] who
reported a substantial increase in the total bed expansion
with pressure increase up to 1500 kPa.
Values of the voidage at minimum bubbling emb were
determined from bed height measurements. In this study, the
bed voidage at minimum bubbling for FCC catalyst was
found to increase from 0.47 at ambient conditions to 0.49 at
1000 kPa. Similar small increases caused by pressure was
noticed for some Geldart A materials by other workers
[11,18,49,57–59]. Piepers et al. [26] observed slightly
greater increase in the minimum bubbling voidage for 59-
Am sized catalyst within the similar pressure range (from
0.58 at atmospheric pressure to 0.63 at 1500 kPa).
3.5. Bubbling bed voidage at elevated pressure
For FCC catalyst and silica sand the ECT system
generated two types of data:
� time series image frames of the local solids volume
fraction distribution at a given horizontal level in the
form of a 32� 32 pixels matrix;� time series data points of the average solids volume
fraction representing the whole bed at a given horizontal
level.
Fig. 5. Variation of the maximum bed expansion ratio with pressure for Geldart
predictions from the Abrahamsen and Geldart [20] correlation.
It is accepted that the tomographic images obtained from
the capacitance measurements are usually of relatively low
resolutzion (e.g. Refs. [60–62]). A linear back-projection
algorithm, supplied as standard with the PTL300 system, is
mathematically simple and fast because the image recon-
struction process is reduced to matrix–vector multiplication.
However, the images are only approximate and suffer from
blurring. Although, image resolution and accuracy can be
improved by employing an iterative linear back-projection
algorithm, this and other reconstruction algorithms are still
under development [61,63–65].
According to the Process Tomography Application Note
[66], the linear back-projection algorithm will always un-
derestimate areas of high permittivity and overestimate areas
of low permittivity. The images produced by this method
will always be approximate, since the method spreads the
true image over the whole sensor area. Because the image
has been spread out over the whole area, the magnitude of
the image pixels will be less than the true values. However,
the sum of all of the pixels will approximate to the true
value, and the linear back-projection algorithm is therefore
useful for calculating the average voidages.
At each operating pressure, measurements of relative
solids volume fraction were taken at a number of superficial
gas velocities above the minimum fluidization velocity. At
each given gas velocity, 16,000 frames of data were logged
over more than 3 min of dynamic operation and recorded by
the ECT system at the rate of approximately 81 frames per
second. The output, which was in the form of 32� 32 pixels
matrix was averaged and provided for each frame the
average volume fraction as a single value between 0 (gas)
and 100 (packed bed). From 16000 values of the relative
voidage and the sample frequency the relevant time series
statistics were calculated.
A FCC catalyst. Comparison of experimental values (clear squares) with
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 145
Three parameters were selected for further analysis—
average, average absolute deviation and average cycle
frequency. Although some analysis techniques were origi-
nally proposed for pressure fluctuations time series, in this
work they have been applied to the analysis of the voidage
fluctuations resulting from the ECT measurements. Accord-
ing to Schouten et al. [67], the average absolute deviation of
the data points from the solids volume fraction average
value is a robust estimator of the width of time series around
the mean. According to Zijerveld et al. [68], the average
absolute deviation is comparable with the standard deviation
and shows similar dependence on operating conditions. The
average cycle frequency is the reciprocal of the average
cycle time, which is defined as the average time to complete
a full cycle after the first passage through the time series
average. These three parameters make it possible to com-
pare results between measurements at various gas velocities
and different operating pressures, since their values are
unambiguous and can be readily calculated. The time series
data were also used in the reconstruction of an attractor from
which the Kolmogorov entropy was estimated for use in
chaos analysis.
3.5.1. Average total bed voidage
The experimental values of the average relative solids
volume fraction were expressed in percentage points, and
under the existing operating conditions fluctuated some-
where between 100 in a non-fluidized state and 55 in a
bubbling regime. The value of 100 was established during
the calibration procedure and corresponded to a packed bed.
Based on a known packed bed height, the packed bed
voidage was calculated to be equal to 0.476 for the FCC
catalyst and 0.463 for the silica sand. For both materials,
calibration procedures were completed at various operating
Fig. 6. Variation in average bed voidage with gas velocity for FCC catalyst over a
the eye).
pressures and the packed bed height, and therefore voidage,
did not vary with pressure.
Fig. 6 shows the measured influence of superficial gas
velocity and operating pressure on the average bed voidage
for FCC catalyst. Average bed voidage reduces with in-
creasing gas velocity above the minimum bubbling velocity
of 0.006 m/s and up to about 0.03 m/s, and generally
increases thereafter. This result is consistent with the find-
ings of other researchers at ambient pressure [44,45,69,70]
who found that at superficial gas velocities up to 0.03 m/s
the bed voidage decreases with increase in gas velocity.
It might be expected that the total bed expansion would
increase if more gas is put into the fluidized bed as bubbles.
However, according to Geldart et al. [69], the reduction in
the bed expansion just above the minimum bubbling veloc-
ity in Geldart A powders occurs because the dense phase
volume in the bubbling bed is reduced more rapidly than the
bubble hold-up increases. According to Geldart and Radtke
[70], this reduction in dense phase voidage is due to small
interparticle forces which make the powder slightly cohe-
sive and are continually disrupted by the bubbles passage
and increase in powder circulation.
The effect of operating pressure on the cross-section
averaged total bed voidage for the Geldart A FCC catalyst
can be clearly seen in Fig. 6. This diagram shows that any
pressure increase is accompanied by the reduction of the
average bed voidage.
The ECT system used in this work can only provide
information about the total bed voidage, consisting of the
dense phase voidage and bubbles volume held up within the
bed and averaged across one cross-sectional plane. There-
fore, based on these results alone, we cannot determine
whether the decrease in the bed voidage with the increase in
operating pressure, seen in Fig. 6, is caused by a reduction
range of operating pressures from 300 to 1900 kPa (lines are used to guide
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154146
in dense phase voidage or volume of bubbles in the bed, or
both.
However, the bed collapse experiments (see below)
demonstrate that for FCC catalyst the dense phase voidage
increased with the increase in pressure. The decrease in the
bubbling bed voidage or expansion with increase in pres-
sure, found in this work from the ECT dynamic measure-
ments, can therefore be explained by the reduction in
volume of bubbles held up within the bed at higher
operating pressures.
This might be in line with the observations of other
researchers [24,59,71–75], who reported that fluidization
became smoother at higher pressures and attributed that to
smaller bubbles in Geldart A powders at increased pressure.
However, in the present work, because of the ECT limi-
tations in image generating, no conclusion on the volume or
size of individual bubbles could be reached.
The results of the ECT experiments with the Geldart B
silica sand are different from those for the FCC catalyst. As
can be seen in Fig. 7, a considerable increase in the bed
voidage with increasing gas velocity takes place at each
operating pressure. This is expected as more gas is put into
the fluidized bed as bubbles. In comparison to Geldart A
powders, the interparticle forces in Geldart B materials are
negligible compared with the hydrodynamic forces acting in
the fluidized bed.
Fig. 7 also shows that increase in operating pressure
produces an increase in average bed voidage, consistent
with the trends reported for Geldart B powders by other
workers [8,9].
However, some unexplained changes in bed expansion
at higher pressures were observed by Olowson and Alm-
stedt [76] and Llop et al. [13,77], who fluidized silica
sand and found that the bed expansion strongly increased
with pressure up to a maximum at approximately 800 kPa
and then stayed constant or even slightly decreased
Fig. 7. Variation in average bed voidage with gas velocity for silica sand
thereafter at pressures up to 1600 kPa. Although in the
present work, no obvious decrease in total bed voidage
was observed at higher operating pressures, it was found
that the pressure influence was stronger at lower pressures
(see Fig. 7).
Olowson and Almstedt [78] found in their fluidization
work with Geldart B sand that the bubble size is deter-
mined by a complex balance between splitting and coa-
lescence, and an increase in pressure may cause either
increase or decrease in bubble size, depending on the
location in the bed, gas velocity and the pressure level.
In a comprehensive summary and analysis of previous
research on bubble size under pressurized conditions,
applicable for the pressurized fluidized bed combustion,
Cai et al. [79] reached the conclusion that in fluidized beds
of coarse materials the bubble size decreases with increas-
ing pressure except when gas velocity is low. At low gas
velocities, there is a dual effect of pressure on bubble size,
i.e. there is an initial increase in bubble size in the pressure
range less than 1000 kPa and then a size decrease with
further increase in pressure. The bed voidage results,
obtained from the dynamic ECT data in this study, are
therefore in accordance with the views of Olowson and
Almstedt [78] and Cai et al. [79].
3.5.2. Average absolute deviation
In bubbling fluidized beds the main source of signal
(pressure or voidage) fluctuations originates from the for-
mation of bubbles. The intensity of the signal can be
measured and compared in a statistical manner by using
the average absolute deviation. Therefore it was expected
that the average absolute deviation in the bed voidage would
steadily increase with increasing gas velocity when more
and more gas is put into the bed as bubbles. This was indeed
the case for both Geldart A and Geldart B materials, as can
be seen in Figs. 8 and 9.
over a range of operating pressures from atmospheric to 1700 kPa.
Fig. 8. Variation in average absolute deviation in bed voidage with gas velocity for FCC catalyst over a range of operating pressures from 300 to 1900 kPa
(lines are used to guide the eye).
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 147
For the Geldart A FCC catalyst (Fig. 8) average absolute
deviations of bed voidage was found to increase steadily
with gas velocity, as expected, and decrease with increasing
operating pressure—this effect being stronger at lower
pressure, as was found for average bed voidage. The
decrease in average absolute deviations of bed voidage with
increasing operating pressure is consistent with smaller
bubble size at higher pressures.
For the Geldart B silica sand, as can be seen in Fig. 9,
increasing operating pressure from ambient to 2100 kPa
has practically no effect on the average absolute deviation
in bed voidage and bubbling behavior of the bed. Once
again, the fluidized bed remains in the bubbling state
within the range of gas velocities studied, as can be seen
Fig. 9. Variation in average absolute deviation in bed voidage with gas velocity
2100 kPa.
from the increase in the average absolute deviation with
increasing gas velocity.
3.5.3. Average cycle frequency
The dependence of the measured average cycle frequen-
cy on gas velocity and operating pressure for the Geldart A
FCC catalyst and the Geldart B silica sand is shown in Figs.
10 and 11, respectively.
For the Geldart A FCC catalyst the average cycle
frequency is found to be variable at low gas velocities,
but tend towards a steady value once the bed was freely
bubbling (Umf is approximately 0.003 m/s and Umb is
approximately 0.006 m/s). Similar large differences between
different pressure fluctuations measurements at velocities
for silica sand over a range of operating pressures from atmospheric to
Fig. 10. Variation in average cycle frequency with gas velocity for FCC catalyst over a range of operating pressures from 300 to 1900k Pa (lines are used to
guide the eye).
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154148
near to Umf and Umb were observed at ambient conditions
by van der Stappen et al. [80] and Daw and Halow [81].
It can be seen from Fig. 10 that average cycle frequency
decreases from 4.5 Hz at 300 kPa to 2.3 Hz at 1900 kPa. We
note that the influence of pressure on the average cycle
frequency is stronger at low pressures, as was the case for
average bed voidage and average absolute deviation in
voidage. According to Bai et al. [82], experimental results
presented by van der Stappen et al. [83] suggest that higher
cycle frequencies correspond to more complex dynamic
systems. Therefore, the ECT experimental results, presented
in Fig. 10, show that increasing the operating pressure leads
Fig. 11. Variation in average cycle frequency with gas velocity for silica sand over
to guide the eye).
to a less dynamic fluidized bed system in line with other
researchers’ observations of smoother fluidization for Gel-
dart A materials at high pressure, which is generally
attributed to smaller bubbles.
For the Geldart B silica sand, in the intermediate regime
near the minimum fluidization and at gas velocities below
approximately 0.04 m/s, the average cycle frequency is
very sensitive and the differences between different meas-
urements are quite large, as shown in Fig. 11. When the
bubbling bed is developed, the average cycle frequency of
voidage fluctuations is about constant at a value of about
3.2 Hz at all the operating pressures tested in the range
a range of operating pressures from atmospheric to 2100 kPa (lines are used
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 149
from atmospheric to 2100 kPa. Similarly, the constant
value of the average cycle frequency of pressure fluctua-
tions of about 3.3 Hz in a bubbling bed was reported by
van der Stappen et al. [80] who fluidized Geldart B
polystyrene particles at ambient conditions. From Fig.
11, it can be observed that in the fully developed bubbling
regime the average cycle frequency is practically indepen-
dent of pressure.
3.5.4. Deterministic chaos analysis
Recently it has been suggested that the irregular behavior
of the fluidized bed dynamics is due to the fact that the
fluidized bed is a chaotic non-linear system. According to
some researchers in this area [68,84], chaotic systems are
governed by non-linear interactions between the system
variables and all methods of non-linear chaos analysis are
based on the construction of an attractor of the system in
state-space. The attractor forms a fingerprint of the system
and reflects its hydrodynamic state. The most common
method to characterize the attractor is the evaluation of
the correlation dimension and the Kolmogorov entropy,
where the correlation dimension expresses the number of
degrees of freedom of the system and the Kolmogorov
entropy is a measure of the predictability of the system
and the sensitivity to the initial state.
The Kolmogorov entropy, K, is a number expressed in
bits/s and can be calculated from a time series of only one
characteristic variable of the system, solids volume fraction
in this case. Generally, the Kolmogorov entropy is small in
cases of more or less regular behavior, and large for very
irregular dynamic behavior such as fluctuations in turbulent
flow.
The average absolute deviation is a measure of the
characteristic length and the average cycle frequency is a
Fig. 12. Kolmogorov entropy as a function of gas velocity for FCC catalyst over a
the eye).
measure of the time scale in the time series, and both
invariants were used in the reconstruction of the attractor,
from which the Kolmogorov entropy was calculated. Since
for the Geldart B material studied, both invariants were
found to be practically independent of pressure, it is
expected that the Kolmogorov entropy for this material
would be also more or less unaffected by pressure.
In order to observe the dynamic processes in fluidized
beds and be able to apply fully a chaotic time series
analysis, Daw and Halow [81] recommend acquiring time
series fluidized bed pressure drop or voidage measurements
at an optimum sampling rate of 200 Hz. Schouten and van
den Bleek [85] have found that in order to sufficiently
accommodate the chaos analysis attractor in its state space,
the required sampling frequency should be at approximately
100 times the average cycle frequency. Based on the average
cycle frequency of 3.2 Hz for the bubbling bed of the
Geldart B sand, the required sampling frequency should be
more than 300 Hz.
However, the ECT system used in this work was not
capable of sampling frequency above 90 Hz. Taking into
consideration this limitation of the equipment, it was ac-
cepted that the chaos analysis of the experimental data
might not be complete. According to Kuehn et al. [86], a
number of points per cycle in the voidage time series from
the ECT measurements is rather low which may lead to an
over-estimation of the Kolmogorov entropy. The Kolmo-
gorov entropy calculated from the results of the ECT
experiments with the Geldart A material is presented in
Fig. 12.
As can be seen in Fig. 12, at minimum bubbling
(Umbg0.006 m/s), the Kolmogorov entropy seems to have
a minimum, generally less than 5 bits per second, which is
lower than in the freely bubbling state. This is in good
range of operating pressures from 300 to 1900 kPa (lines are used to guide
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154150
agreement with results of van der Stappen et al. [80], who
qualitatively explained this in the following way—at gas
velocities where the first bubbles appear, the bubbles are
independent of each other and rise through the bed with no
or minor interaction. This behavior is relatively simpler and
more periodic compared to the developed bubbling state,
where bubbles are influencing each other in a more complex
way.
In the freely bubbling state, the Kolmogorov entropy is
expected to settle at a certain value, which could be as high
as 32 at the operating pressure of 300 kPa or as low as 12 at
1900 kPa. However, because of the equipment limitations
previously explained, Fig. 12 shows possibly not the abso-
lute values but merely trends. Examination of Fig. 12 alone
does not yield any trends. However, we could reasonably
make the comparison with the results for average cycle
frequency (Fig. 10), where the trend established itself at gas
velocities beyond 0.03 m/s. The variation in Kolmogorov
entropy with operating pressure may therefore be revealed
by the final data point in each series—i.e. Kolmogorov
entropy decreases with increasing pressure.
When the Kolmogorov entropy decreases, the fluidized
bed hydrodynamics become more predictable. Zijerveld et
al. [68] explain this in terms of an increase in bubble size at
the bed surface. This is in agreement with Schouten et al.
[87], who related the Kolmogorov entropy K to the bubble
size db as follows:
K ¼ 1:5ðU � Umf ÞDd2b
ð3Þ
According to this equation, the Kolmogorov entropy
decreases with an increase in bubble size. Based on this
and the trends presented for the Geldart A material in Fig.
12, it appears that the bubble size increases with increasing
pressure. However, this is contradictory to the previous
research and the results of this study presented in Fig. 6.
As previously mentioned, generally it has been reported
that fluidization becomes smoother with high pressure, which
has been attributed to smaller bubbles at increased pressure.
Many workers found that increasing the operating pressure
causes bubble size to decrease in Geldart A materials
[24,58,71–75]. A possible explanation might be that Eq.
(3) was developed based on the pressure fluctuations
obtained during the experiments with coarse Geldart B
polyethylene particles (0.56 mm) and silica sand (0.4 mm)
carried out at ambient conditions. As previouslymentioned, it
was found that bubbling behavior in fluidized beds of coarse
Geldart B materials differs noticeably from that in fluidized
beds of Geldart A powders even at ambient conditions.
Even with the Geldart B materials, there are some
apparently conflicting reports coming from the same school.
For example, Zijerveld et al. [68] found that in the bubbling
bed the Kolmogorov entropy decreases with superficial gas
velocity and decreases with an increase in bubble size.
Earlier van der Stappen et al. [80] found that in a freely
bubbling bed the Kolmogorov entropy settles at a value of
about 17 bits per second. In another related study [86],
higher gas velocity and more turbulent hydrodynamics was
found to cause an increase of the Kolmogorov entropy,
though bubble size in Geldart B powders is known to
increase with gas velocity.
Obviously, deterministic chaos theory can provide nu-
merical and graphical tools that can quantify and visualize
the fluidized bed hydrodynamics, however, it is still in its
early days and much more work has to be done. It is
necessary to verify further the correlations and incorporate
other particle systems. So far, it seems that the chaos
analysis method has been mainly applied to scale-up of
the dynamic behavior of the fluidized bubbling reactors and
fluidization regime transitions in the circulating fluidized
beds [68,87].
3.6. Bed collapse tests
Bed collapse experimental results had been obtained in a
form of video recording, from which the plots of bed height
decrease with time were constructed. The results of the
second intermediate stage when the bed surface falls at a
constant rate of collapse velocity Uc, until the bed height
approaches a certain critical height Hc, are plotted in Fig. 13.
It should be noted that the error bars for the curve at
atmospheric pressure are based on the total of 20 experi-
ments, five for each of four initial fluidization gas velocities.
Similar collapse curves for a FCC catalyst at various
operating pressures were observed by Foscolo et al. [49].
The straight line portions of the bed collapse curves were
extrapolated back to time zero and it was assumed that the
intercept with the bed height axis gives the height which the
dense phase would occupy in the bubbling bed.
Abrahamsen and Geldart [45] correlated the dense phase
expansion (Eq. (4)) which includes the gas density effect.
Hd
Hmf
¼2:54q0:016
g l0:066expð0:09ÞFd0:1p g0:118ðqp � qgÞ0:118H0:043
mf
ð4Þ
According to this correlation, the dense phase expansion
should slightly increase with increasing the operating pres-
sure. A comparison between the dense phase expansion
determined experimentally from the bed collapse tests at
various operating pressures and that predicted from the
correlation by Abrahamsen and Geldart [45] is presented
in Fig. 14. For comparison with the maximum non-bubbling
bed expansion for this material shown in Fig. 5, the scale of
both graphs is the same.
As can be seen in Fig. 14, the dense phase expansion
linearly increases with increasing pressure within the stud-
ied range 101–1600 kPa. Compared to the predictions of
the correlation by Abrahamsen and Geldart [45], the exper-
imental results show a slightly higher rate of increase, and
therefore, a stronger influence of operating pressure than the
factor qg0.016 included in the correlation.
Fig. 13. Bed surface collapse curves for FCC catalyst at various operating absolute pressures.
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 151
Similar results were observed by other workers [24,26].
As noted by Barreto et al. [88], the extensive experiments of
Abrahamsen and Geldart were carried out with air at
atmospheric pressure and the effect of gas density arose as
a consequence of the correlation method. According to the
correlation, it was expected that a pressure increase from
atmospheric to 1500 kPa should cause only 4.5% increase in
the dense phase height for a FCC catalyst fluidized with
nitrogen [26]. However, their experimental results demon-
strated a much higher 21% increase. Weimer and Quarderer
[24] also found that the correlation proposed by Abraham-
sen and Geldart [45] largely underestimated the effect of
pressure on the dense phase voidage for a Geldart A powder.
Fig. 14. Variation of the dense phase expansion with pressure for FCC catalyst. C
Abrahamsen and Geldart [45] correlation.
Bed collapse experiments are primarily intended to
obtain a direct value of the dense phase voidage. Once the
initial heights of the dense phase of the bed had been
determined from the collapse curves obtained at various
operating pressures (Fig. 13), the experimental values of the
dense phase voidage ed were calculated. The experimental
values of all the voidages—dense phase voidage, settled bed
voidage, minimum bubbling voidage and minimum fluid-
ization voidage—can now be compared (Fig. 15).
As can be seen in Fig. 15, within the studied pressure
range, the dense phase voidage was found to be higher
than the voidage at minimum fluidization and to increase
steadily with increasing pressure for a Geldart A powder.
omparison of experimental values (clear squares) with predictions from the
Fig. 15. Variation with pressure of dense phase voidage (ed), settled bed voidage (es), minimum fluidization voidage (emf) and minimum bubbling voidage (emb)
for FCC catalyst.
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154152
This is in line with the observations of other researchers
[24,26,49,58,71].
4. Conclusions
A comprehensive experimental study of the influence of
pressure on fluidization phenomena, such as minimum
fluidization and minimum bubbling velocities, bed expan-
sion and voidage was carried out in a bubbling fluidized bed
over the range of operating absolute pressures 101–2100
kPa with Geldart A and B bed materials.
As expected, it was found that the minimum fluidization
velocity decreased slightly with increasing pressure for a
Geldart B material and was independent of pressure for a
Geldart A material. In the pressure range studied in this
work, bed voidage at minimum fluidization was found to be
practically independent of pressure for both Geldart A and
Geldart B materials.
Although it has been implied that with pressure increase
Geldart B solids could demonstrate Geldart A type behavior,
in this work, we observed no shift in behavior over the
pressure range studied.
For the Geldart A powder, the minimum bubbling
velocity and the maximum bed expansion ratio were found
to be practically unaffected by increasing pressure. Predic-
tions using existing correlations for the minimum bubbling
velocity and the maximum bed expansion ratio were not in
agreement with the experimental values. In line with obser-
vations of other researchers, bed voidage at minimum
bubbling was found to increase slightly within the studied
pressure range.
Electrical capacitance tomography was used to provide a
time series analysis of fluctuations of the average solids
volume fraction, from which a quantitative description of
the bubbling bed dynamics as a function of operating
pressure was obtained. For Geldart A catalyst, it was found
that average bed voidage decreased with increasing operat-
ing pressure. For Geldart B sand, however, the opposite
trend was observed.
The intensity of the voidage fluctuations caused by the
formation of bubbles was measured and compared by using
the average absolute deviation. For Geldart A material,
increase in operating pressure gave rise to a decrease in
the average absolute deviation in bed voidage, suggesting
more uniform bubbling at elevated pressure. For Geldart B
material, increasing pressure up to 2100 kPa had no effect
on the average absolute deviation in voidage fluctuations.
For Geldart A material, the average cycle frequency
decreased with increasing operating pressure. This sug-
gested that increasing the operating pressure lead to a less
dynamic fluidized bed system in line with other researchers’
observations of smoother fluidization for Geldart A materi-
als at high pressure. For Geldart B solids, the average cycle
frequency was found to be independent of pressure.
Bed collapse tests were carried out at various pressures
up to 1600 kPa, using Geldart A solids. The dense phase
voidage values derived from these experiments were found
to be higher than the values of voidage at minimum
fluidization and were found to increase steadily with in-
creasing pressure.
References
[1] M.I. Fridland, The effect of pressure on productivity and on entrain-
ment of particles in fluidized bed equipment, Int. Chem. Eng. 3 (4)
(1963) 519–522.
[2] J.S.M. Botterill, Fluidized bed behaviour at high temperatures and
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154 153
pressures, in: L.K. Doraiswamy, A.S. Mujumdar (Eds.), Transport in
Fluidized Particle Systems, Elsevier, Amsterdam, 1989, pp. 33–70.
[3] T.M. Knowlton, Pressure and temperature effects in fluid–particle
systems, in: W.C. Yang (Ed.), Fluidization Solids Handling and Pro-
cessing: Industrial Applications, Noyes Publications, Westwood,
1999, pp. 111–152.
[4] I. Sidorenko, M.J. Rhodes, Pressure effects on gas–solid fluidized
bed behavior, Int. J. Chem. React. Eng. 1 (2003) R5.
[5] J.G. Yates, Review article number 49. Effects of temperature and
pressure on gas–solid fluidization, Chem. Eng. Sci. 51 (2) (1996)
167–205.
[6] V.A. Borodulya, V.L. Ganzha, V.I. Kovensky, Gidrodynamika i
teploobmen v psevdoozhizhenom sloye pod davleniem (in Russian),
Nauka i Technika, Minsk, 1982.
[7] R. Bouratoua, Y. Molodtsof, A. Koniuta, ‘‘Hydrodynamic character-
istics of a pressurized fluidized bed’’. Paper presented at 12th Inter-
national Conference on Fluidized Bed Combustion, La Jolla, 1993.
[8] S. Chiba, J. Kawabata, T. Chiba, Characteristics of pressurized gas-
fluidized beds, in: N.P. Cheremisinoff (Ed.), Encyclopedia of Fluid
Mechanics, Gulf Publishing, Houston, 1986, pp. 929–945.
[9] D.C. Chitester, R.M. Kornosky, L.S. Fan, J.P. Danko, Characteristics of
fluidization at high pressure, Chem. Eng. Sci. 39 (2) (1984) 253–261.
[10] M.A. Gilbertson, D.J. Cheesman, J.G. Yates, Observations and meas-
urements of isolated bubbles in a pressurized gas-fluidized bed, in:
L.S. Fan, T.M. Knowlton (Eds.), Fluidization IX, Engineering Foun-
dation, New York, 1998, pp. 61–68.
[11] D.F. King, D. Harrison, The dense phase of a fluidized bed at elevated
pressures, Trans. Inst. Chem. Eng., (1) (1982) 26–30.
[12] T.M. Knowlton, High-pressure fluidization characteristics of several
particulate solids, primarily coal and coal-derived materials, AIChE
Symp. Ser. 73 (161) (1977) 22–28.
[13] M.F. Llop, J. Casal, J. Arnaldos, Incipient fluidization and expansion
in fluidized beds operated at high pressure and temperature, in: J.-F.
Large, C. Laguerie (Eds.), Fluidization VIII, Engineering Foundation,
New York, 1995, pp. 131–138.
[14] A. Marzocchella, P. Salatino, Fluidization of solids with CO2 at pres-
sures from ambient to supercritical, AIChE J. 46 (5) (2000) 901–910.
[15] M. Nakamura, Y. Hamada, S. Toyama, A.E. Fouda, C.E. Capes, An
experimental investigation of minimum fluidization velocity at ele-
vated temperatures and pressures, Can. J. Chem. Eng. 63 (1) (1985)
8–13.
[16] P.A. Olowson, A.E. Almstedt, Influence of pressure on the minimum
fluidization velocity, Chem. Eng. Sci. 46 (2) (1991) 637–640.
[17] S.C. Saxena, G.J. Vogel, The measurement of incipient fluidization
velocities in a bed of coarse dolomite at temperature and pressure,
Trans. Inst. Chem. Eng. 55 (3) (1977) 184–189.
[18] L.E.L. Sobreiro, J.L.F. Monteiro, The effect of pressure on fluidized
bed behavior, Powder Technol. 33 (1982) 95–100.
[19] C. Vogt, R. Schreiber, J. Werther, G. Brunner, Fluidization at super-
critical fluid conditions, in: M. Kwauk, J. Li, W.C. Yang (Eds.),
Fluidization X, United Engineering Foundation, New York, 2001,
pp. 117–124.
[20] A.R. Abrahamsen, D. Geldart, Behavior of gas-fluidized beds of fine
powders: part I. Homogeneous expansion, Powder Technol. 26 (1980)
35–46.
[21] K.V. Jacob, A.W. Weimer, High-pressure particulate expansion and
minimum bubbling of fine carbon powders, AIChE J. 33 (10) (1987)
1698–1706.
[22] A.K. Bin, Minimum fluidization velocity at elevated temperatures and
pressures, Can. J. Chem. Eng. 64 (5) (1986) 854–857.
[23] W.C. Yang, D.C. Chitester, R.M. Kornosky, D.L. Keairns, A general-
ized methodology for estimating minimum fluidization velocity at el-
evated pressure and temperature, AIChE J. 31 (7) (1985) 1086–1092.
[24] A.W. Weimer, G.J. Quarderer, On dense phase voidage and bubble
size in high pressure fluidized beds of fine powders, AIChE J. 31 (6)
(1985) 1019–1028.
[25] P.N. Rowe, The dense phase voidage of fine powders fluidised by gas
and its variation with temperature, pressure and particle size, in: J.R.
Grace, L.W. Shemilt, M.A. Bergougnou (Eds.), Fluidization VI, En-
gineering Foundation, New York, 1989, pp. 195–202.
[26] H.W. Piepers, E.J.E. Cottaar, A.H.M. Verkooijen, K. Rietema, Effects
of pressure and type of gas on particle–particle interaction and the
consequences for gas–solid fluidization behavior, Powder Technol.
37 (1984) 55–70.
[27] C. Vogt, R. Schreiber, J. Werther, G. Brunner, ‘‘The expansion be-
havior of fluidized beds at supercritical fluid conditions’’. Paper pre-
sented at World Congress on Particle Technology 4, Sydney, 2002.
[28] D. Geldart, Single particles, fixed and quiescent beds, in: D. Gel-
dart (Ed.), Gas Fluidization Technology, Wiley, Chichester, 1986,
pp. 11–32.
[29] J.G. Yates, Experimental observations of voidage in gas fluidized
beds, in: J. Chaouki, F. Larachi, M.P. Duducovic (Eds.), Non-Inva-
sive Monitoring of Multiphase Flows, Elsevier, Amsterdam, 1997,
pp. 141–160.
[30] D. Geldart, H.Y. Xie, The collapse test as a means for charac-
terizing Group A powders (preprints), in: J.-F. Large, C. Laguerie
(Eds.), Fluidization VIII, Engineering Foundation, Tours, 1995,
pp. 263–270.
[31] J.R. Grace, Agricola aground: characterization and interpretation of
fluidization phenomena, AIChE Symp. Ser. 88 (289) (1992) 1–16.
[32] K. Rietema, The Dynamics of Fine Powders, Elsevier, London, 1991.
[33] M. Louge, Experimental techniques, in: J.R. Grace, A.A. Avidan,
T.M. Knowlton (Eds.), Circulating Fluidized Beds, Blackie, London,
1997, pp. 312–368.
[34] D. Geldart, Types of gas fluidization, Powder Technol. 7 (1973)
285–292.
[35] J.S. Halow, P. Nicoletti, Observations of fluidized bed coalescence
using capacitance imaging, Powder Technol. 69 (1992) 255–277.
[36] Y.T. Makkawi, P.C. Wright, ‘‘Application of process tomography as a
tool for better understanding of fluidization quality in a conventional
fluidized bed’’. Paper presented at 2nd World Congress on Industrial
Process Tomography, Hannover, 2001.
[37] S.J. Wang, T. Dyakowski, C.G. Xie, R.A. Williams, M.S. Beck, Real
time capacitance imaging of bubble formation at the distributor of a
fluidized bed, Chem. Eng. J. 56 (3) (1995) 95–100.
[38] I. Sidorenko, M.J. Rhodes, ‘‘The use of Electrical Capacitance Tomog-
raphy to study the influence of pressure on fluidized bed behaviour’’.
Paper presented at 6th World Congress of Chemical Engineering,
Melbourne, 2001.
[39] L. Svarovsky, Powder Testing Guide: Methods of Measuring the
Physical Properties of Bulk Powders, Elsevier, London, 1987.
[40] Engineering design rules for ECT sensors (Wilmslow, Process To-
mography), 2001a.
[41] I. Sidorenko, Pressure Effects on Fluidized Bed Behaviour, PhD the-
sis, Monash University, Clayton, 2003.
[42] J.V. Fletcher, M.D. Deo, F.V. Hanson, Fluidization of a multi-sized
Group B sand at reduced pressure, Powder Technol. 76 (1993)
141–147.
[43] P. Harriott, S. Simone, Fluidizing fine powders, in: N.P. Cheremisinoff,
R. Gupta (Eds.), Handbook of Fluids in Motion, Science, Ann Arbor,
1983, pp. 653–663.
[44] D. Geldart, A.C.-Y. Wong, Fluidization of powders showing degrees
of cohesiveness: II. Experiments on rates of de-aeration, Chem. Eng.
Sci. 40 (4) (1985) 653–661.
[45] A.R. Abrahamsen, D. Geldart, Behavior of gas-fluidized beds of fine
powders: part II. Voidage of the dense phase in bubbling beds, Pow-
der Technol. 26 (1980) 47–55.
[46] C.Y. Wen, Y.H. Yu, A generalized method for predicting the minimum
fluidization velocity, AIChE J. 12 (3) (1966) 610–612.
[47] S. Ergun, Fluid flow through packed columns, Chem. Eng. Prog. 48
(1952) 89–94.
[48] J. Werther, Stromungsmechanische grundlagen der wirbelschichttech-
nik (in German), Chem. Ing. Tech. 49 (3) (1977) 193–202.
[49] P.U. Foscolo, A. Germana, R. Di Felice, L. De Luca, L.G. Gibilaro,
I. Sidorenko, M.J. Rhodes / Powder Technology 141 (2004) 137–154154
An experimental study of the expansion characteristics of fluidized
beds of fine catalysts under pressure, in: J.R. Grace, L.W. Shemilt,
M.A. Bergougnou (Eds.), Fluidization VI, Engineering Foundation,
New York, 1989, pp. 187–194.
[50] P.N. Rowe, P.U. Foscolo, A.C. Hoffmann, J.G. Yates, Fine powders
fluidized at low velocity at pressures up to 20 bar with gases of
different viscosity, Chem. Eng. Sci. 37 (7) (1982) 1115–1117.
[51] M. Sciazko, J. Bandrowski, Effect of pressure on the minimum bub-
bling velocity of polydisperse materials, Chem. Eng. Sci. 40 (10)
(1985) 1861–1869.
[52] M. Sciazko, J. Bandrowski, Effect of pressure on the minimum bub-
bling velocity of polydisperse materials. Reply to comments, Chem.
Eng. Sci. 42 (2) (1987) 388.
[53] T. Varadi, J.R. Grace, High pressure fluidization in a two-dimensional
bed, in: J.F. Davidson, D.L. Keairns (Eds.), Fluidization, Cambridge
Univ. Press, Cambridge, 1978, pp. 55–58.
[54] J. Baeyens, D. Geldart, Predictive calculations of flow parameters in
gas fluidized beds and fluidization behavior of various powders, in:
H. Angelino, J.P. Couderc, H. Gibert, C. Laguerie (Eds.), Fluidization
and its Application, Societe de Chimie Industrielle, Toulouse, 1974,
pp. 263–273.
[55] M.E. Crowther, J.C. Whitehead, Fluidization of fine particles at ele-
vated pressure, in: J.F. Davidson, D.L. Keairns (Eds.), Fluidization,
Cambridge Univ. Press, Cambridge, 1978, pp. 65–70.
[56] J.F. Richardson, Incipient fluidization and particulate systems, in:
J.F. Davidson, D. Harrison (Eds.), Fluidisation, Academic Press, Lon-
don, 1971, pp. 25–64.
[57] K. Godard, J.F. Richardson, The behaviour of bubble-free fluidised
beds, IChemE Symp. Ser. 30 (1968) 126–135.
[58] J.R.F. Guedes de Carvalho, Dense phase expansion in fluidized beds
of fine particles. The effect of pressure on bubble stability, Chem.
Eng. Sci. 36 (2) (1981) 413–416.
[59] J.R.F. Guedes de Carvalho, D.F. King, D. Harrison, Fluidization of
fine particles under pressure, in: J.F. Davidson, D.L. Keairns (Eds.),
Fluidization, Cambridge Univ. Press, Cambridge, 1978, pp. 59–64.
[60] M. Byars, ‘‘Developments in Electrical Capacitance Tomography’’.
Paper presented at 2nd World Congress on Industrial Process Tomog-
raphy, Hannover, 2001.
[61] T. Dyakowski, L.F.C. Jeanmeure, A.J. Jaworski, Applications of elec-
trical tomography for gas–solids and liquid–solids flows—a review,
Powder Technol. 112 (2000) 174–192.
[62] Y.T. Makkawi, P.C. Wright, Optimization of experiment span and data
acquisition rate for reliable electrical capacitance tomography mea-
surement in fluidization studies—a case study, Meas. Sci. Technol. 13
(2002) 1831–1841.
[63] T. Dyakowski, personal communication, Clayton, 2002.
[64] O. Isaksen, A review of reconstruction techniques for capacitance
tomography, Meas. Sci. Technol. 7 (3) (1996) 325–337.
[65] O. Isaksen, J.E. Nordtvedt, A new reconstruction algorithm for pro-
cess tomography, Meas. Sci. Technol. 4 (3) (1993) 1464–1475.
[66] Generation of ECT images from capacitance measurements (Wilm-
slow, Process Tomography) 2001b.
[67] J.C. Schouten, F. Takens, C.M. van den Bleek, Estimation of the di-
mension of a noisy attractor, Phys. Rev., E 50 (3) (1994) 1851–1861.
[68] R.C. Zijerveld, F. Johnsson, A. Marzocchella, J.C. Schouten, C.M.
van den Bleek, Fluidization regimes and transitions from fixed bed to
dilute transport flow, Powder Technol. 95 (1998) 185–204.
[69] D. Geldart, N. Harnby, A.C.-Y. Wong, Fluidization of cohesive pow-
ders, Powder Technol. 37 (1984) 25–37.
[70] D. Geldart, A.L. Radtke, The effect of particle properties on the
behavior of equilibrium cracking catalysts in standpipe flow, Powder
Technol. 47 (1986) 157–165.
[71] G.F. Barreto, J.G. Yates, P.N. Rowe, The effect of pressure on the
flow of gas in fluidized beds of fine particles, Chem. Eng. Sci. 38 (12)
(1983) 1935–1945.
[72] I.H. Chan, C. Sishtla, T.M. Knowlton, The effect of pressure on
bubble parameters in gas-fluidized beds, Powder Technol. 53 (1987)
217–235.
[73] D.F. King, D. Harrison, The bubble phase in high-pressure fluidized
beds, in: J.R. Grace, J.M. Matsen (Eds.), Fluidization, Plenum, New
York, 1980, pp. 101–108.
[74] P.N. Rowe, H.J. MacGillivray, A preliminary X-ray study of the effect
of pressure on a bubbling gas fluidised bed, in: Fluidised Combustion:
Systems and Applications, vol. IV-1, Institute of Energy, London,
1980, pp. 1–9.
[75] M.P. Subzwari, R. Clift, D.L. Pyle, Bubbling behavior of fluidized
beds at elevated pressures, in: J.F. Davidson, D.L. Keairns (Eds.),
Fluidization, Cambridge Univ. Press, Cambridge, 1978, pp. 50–54.
[76] P.A. Olowson, A.E. Almstedt, Influence of pressure and fluidization
velocity on the bubble behavior and gas flow distribution in a fluid-
ized bed, Chem. Eng. Sci. 45 (7) (1990) 1733–1741.
[77] M.F. Llop, J. Casal, J. Arnaldos, Expansion of gas–solid fluidized
beds at pressure and high temperature, Powder Technol. 107 (2000)
212–225.
[78] P.A. Olowson, A.E. Almstedt, Hydrodynamics of a bubbling fluidized
bed: influence of pressure and fluidization velocity in terms of drag
force, Chem. Eng. Sci. 47 (2) (1992) 357–366.
[79] P. Cai, M. Schiavetti, G. De Michele, G.C. Grazzini, M. Miccio,
Quantitative estimation of bubble size in PFBC, Powder Technol.
80 (1994) 99–109.
[80] M.L.M. van der Stappen, J.C. Schouten, C.M. van den Bleek, Appli-
cation of deterministic chaos theory in understanding the fluid dy-
namic behavior of gas– solids fluidization, AIChE Symp. Ser. 89
(296) (1993) 91–102.
[81] C.S. Daw, J.S. Halow, Evaluation and control of fluidization quality
through chaotic time series analysis of pressure-drop measurements,
AIChE Symp. Ser. 89 (296) (1993) 103–122.
[82] D. Bai, A.S. Issangya, J.R. Grace, Characteristics of gas-fluidized
beds in different flow regimes, Ind. Eng. Chem. Res. 38 (3) (1999)
803–811.
[83] M.L.M. van der Stappen, J.C. Schouten, C.M. van den Bleek, ‘‘De-
terministic chaos analysis of the dynamical behaviour of slugging and
bubbling fluidized beds’’. Paper presented at 12th International Con-
ference on Fluidized Bed Combustion, La Jolla, 1993.
[84] F. Johnsson, R.C. Zijerveld, J.C. Schouten, C.M. van den Bleek,
B. Leckner, Characterization of fluidization regimes by time-series
analysis of pressure fluctuations, Int. J. Multiph. Flow 26 (4)
(2000) 663–715.
[85] J.C. Schouten, C.M. van den Bleek, Monitoring the quality of fluid-
ization using the short-term predictability of pressure fluctuations,
AIChE J. 44 (1) (1998) 48–60.
[86] F.T. Kuehn, J.C. Schouten, R.F. Mudde, C.M. van den Bleek, B.
Scarlett, Analysis of chaos in fluidization using electrical capaci-
tance tomography, Meas. Sci. Technol. 7 (3) (1996) 361–368.
[87] J.C. Schouten, M.L.M. van der Stappen, C.M. van den Bleek, Scale-
up of chaotic fluidized bed hydrodynamics, Chem. Eng. Sci. 51 (10)
(1996) 1991–2000.
[88] G.F. Barreto, G.D. Mazza, J.G. Yates, The significance of bed col-
lapse experiments in the characterization of fluidized beds of fine
powders, Chem. Eng. Sci. 43 (11) (1988) 3037–3047.