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Axial transport and residence time of MSW in rotary kilns:
Part II. Theoretical and optimal analyses
S.-Q. Li a,b,*, Y. Chi a, R.-D. Li a, J.-H. Yan a, K.-F. Cen a
aDepartment of Energy Engineering, Zhejiang University, Hangzhou 310027, PR ChinabDepartment of Thermal Engineering, Tsinghua University, Beijing 100084, PR China
Received 17 October 2000; received in revised form 28 December 2001; accepted 31 December 2001
Abstract
A novel particulate trajectory model (PTM) is developed to predict axial transport and dispersion of municipal solid wastes (MSW), based
on the vector analysis on particle’s gravity-induced axial displacement in a single excursion. Three parts of work are extended with respect to
this PTM. First, the simplified formulas about mean residence time (MRT) and material volumetric flow (MVF) are derived by incorporating
statistic-averaged analysis on all repeated excursions of solids within kiln into PTM. The correctional factors—et for MRT and ef for MVF—
are introduced to improve the model’s validity under such practical cases, i.e. irregular MSW existence or internal-structure presence.
Reasonable agreement is obtained between the empirical formulas and experiments with correlation factor in excess of 90% for all runs.
Second, a stochastic PTM is extended to predict the residence time distribution (RTD) curves of segregated MSW by considering the
probability of the rolling distance of individual particle. As for MSW, the main cause of axial dispersion is the segregation of rolling distance
of solids, due to variation of MSW components, shapes and sizes. Finally, the optimization model for geometry design of a laboratory-scale
rotary kiln pyrolyser of MSW is presented and the corresponding optimum solutions are provided.
D 2002 Published by Elsevier Science B.V.
Keywords: Rotary kiln; MSW; Axial transport; Particulate trajectory model; Optimization
1. Introduction
The experimental studies of mean residence time (MRT)
and material volumetric flow (MVF) of municipal solid
wastes (MSW) in a technical-scale rotary kiln simulator
have been conducted in Part I. Modeling on the transport
behavior of MSW in rotary kiln provides not only the basis
to simulate heat transfer as well as apparent kinetic of a
continuous reaction, but also the fundamentals to achieve
optimal geometry design of processing.
Henein et al. [1] first classified various forms of solid
motion through a rotary kiln as slipping, slumping, rolling,
cascading, cataracting and centrifuging beds. Generally, the
slipping, slumping and rolling beds often occur in practical
kiln used for MSW incineration or pyrolysis, which are
operated at relatively low rotational speed. In a slipping bed,
the solid particles slide against the kiln wall and the bed acts
as a rigid body with poor axial and lateral mixing. In a
slumping bed, the solids are carried upwards along the
inside wall and reach the upper limit of the angle of repose,
then slump downward by periodic ‘avalanche’ as a segment
of solids detaches itself from the topper half of the bed to the
lower half. In a rolling bed, the solids flow as a continuous
layer, and the inclination angle of the solids is just the
dynamic angle of repose. Of all three beds aforementioned,
the rolling one is the desired case for most kiln operation
due to well mixing of materials. So far, nearly all models on
the solid transport as well as the heat transfer in rotary kilns
are developed in assumption of rolling bed.
Existing models developed to describe the flow and
mixing behaviors of particles in rotary kiln can be generally
classified into two types. One is so-called axial distribution
model (ADM) assuming the solids as ideal fluid. The other
is the single particle trajectory model (PTM) considering
solids as granular substances. Danckwerts [2] pioneered an
axial dispersion model with an appropriate Pe number
determined by experiments. Fan and Ahn [3] first applied
the similar ADM to predict the residence time distribution
(RTD) and dispersion coefficient of solid materials in a
continuous rotary cylinder. Rutgers [4] verified the validity
0032-5910/02/$ - see front matter D 2002 Published by Elsevier Science B.V.
PII: S0032 -5910 (02 )00015 -3
* Corresponding author. Tel.: +86-10-62782108.
E-mail address: [email protected] (S.-Q. Li).
www.elsevier.com/locate/powtec
Powder Technology 126 (2002) 228–240
______________________________________________________________________________________www.paper.edu.cn
of ADM within a case of uniform radial mixing, and
determined the axial dispersion coefficients under varied
conditions of loading, rotational speed, inclination, bed
regimes, shapes of the kiln entrance and exit end faces,
and bulk characteristics of solids. Abouzeid and Fuerstenau
[5] adopted the same ADM to demonstrate its applicability
but noted three explicit premises: the constant axial velocity,
the radial mixing large enough to smooth the concentration
at any cross-section, and the constant dispersion coefficient
for fixed operating conditions. Wes et al. [6] further adjusted
the ADM in a rotary drum system with the remarkable large
Pe number. Mu and Perlmutter [7] developed a novel ADM,
which took into account some of key flow features of the
solids. It simulated the flow by N rolling steps, each
consisting of a flow through a tube followed by a well
mixed vessel with by-pass and recycle. The model contains
three parameters, one of which has to be obtained from RTD
experiments. In addition, Sai et al. [8] and Groen et al. [9]
attempted to use the N tanks-in-series model to fit exper-
imental RTD curves.
As for the PTM, Saeman [10] originally proposed a
model from the geometric analysis of a single particle
trajectory to predict MRT in a shallow rolling kiln. Vahl
and Kigma [11] and Kramers and Croockewit [12] further
confirmed the model validity in a horizontal kiln or
inclined kilns, respectively. The calculation of hold-up as
well as MRT by the modified PTM was considered in their
works. Roger and Gardner [13] extended Saeman’s PTM
and adopted a Monte Carlo simulation to successfully
predict the experimental RTD and axial dispersion for
granular solids in a horizontal rotary drum with variable
bed depth. Hehl et al. [14] initially described the material
behaviors in the kiln applying ADM and PTM simulta-
neously. The ADM was used to evaluate the dispersion
coefficients in the experiments, while MRT and hold-up
were calculated by means of an extended model of Vahl et
al. One disadvantage of Heh’s model is that ADM and
PTM are independent. The work of Gupta and Khakhar
[15] can be regarded as a breakthrough of PTM since
Saeman’s. Starting from kinematics of solids, they deduced
the stochastic evaluation equation for the probability of
rolling distance of a particle within active layer, which is
further incorporated into Saeman’s model to predict RTD
curves. The model predictions were compared with the
experimental data from Hehl et al. and the reasonable
agreement is reached. Similarly, Kohav et al. [16] devel-
oped several stochastic algorithms evaluating the axial or
lateral position of a particle in each rolling step, and
employed them into PTM to predict RTD or axial dis-
persion. An important advantage of Kohav’s model is that
the radial segregation of solids is accounted for. However,
the validity of model is limited to the uniform bed depth
or filling level of solids. Generally, PTM has received
more attention within the last decade by many scholars,
e.g., Gupta and Khakhar [15], Kohav et al. [16], Langrish
[17], Lebas et al. [18], Spuring et al. [19], Afacan and
Masliyah [20]. More recently, Wightman et al. [21]
emphasized the discrete dynamics and colliding interaction
of particles and attempted to use the discrete element
method (DEM) to simulate the flow and mixing of solids
in rotating and rocking cylinder.
The deficiencies of previous models are: (1) The physical
basis of the trajectory of individual particle in a single
rolling step is all from Saeman’s geometrical analysis but
not from the kinematics of the granular flow itself. (2) The
extrapolation of a model developed from homogeneous
particles to highly irregular MSW rarely happens. (3) The
model modification under some special conditions such as
internal-structure presence is seldom considered. (4) The
effect of the solid’s segregation, especially for MSW in an
inclined kiln, is scarcely considered in PTM. (5) An attempt
to extend empirical formulas for MRT and MVF to the
optimization of the geometry design of the system is absent
so far.
In present study, at first, the vector analysis is originally
adopted to account for the gravity-induced axial displace-
ment in a single rolling step, which forms the physical basis
of PTM. Furthermore, three parts of work are extended
elaborately with respect to PTM. First, the empirical for-
mulas on both MRT and MVF are deduced by employing
the statistical-averaged analyses on all rolling steps of
particles into PTM. Two correctional coefficients, et for
MRT and ef for MVF, are proposed to improve model
applicability under practical condition such as a case of
internal-structure presence. Secondly, a stochastic PTM
incorporating the segregation characteristics of MSW is
developed originally to predict detailed RTD curves in an
inclined, bed-depth-varied, continuous rotary kiln. The
simulated RTD of MSW will be compared to the exper-
imental one. Finally, the optimizing model for the geometry
design of a laboratory-scale rotary kiln pyrolyser is pro-
posed and the optimal solutions are discussed.
2. Description of particle trajectory model
2.1. Dynamics of the rolling bed
Before developing the model it is worthwhile to exam-
ine the dynamics of solid materials in a rolling bed. As for
the rolling regime, the bed material is characterized into
two distinct regions shown in Fig. 1(a,c), i.e. the thinner
active layer and the thicker stagnant region under the
former. Particles roll down continually and form a constant
layer on the bed surface, and then enter the stagnant region
where they are carried upward by the rotating wall until
they re-enter the active layer and roll again. The dynamics
of the rolling bed can be vividly depicted as that the
energy imparted by the kiln’s rotation is continuously fed
to solids in the stagnant region as potential energy which is
subsequently dissipated in terms of rolling within the
active layer.
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240 229
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2.2. A gravity-induced particle trajectory model
With regard to the phenomena above, a particle trajectory
model (PTM) is proposed. The solid motion in rotary kiln
consists of many repeated excursions. Every excursion is
composed of two processes, i.e., the particle rolling in the
active layer, and the particle rotation around kiln axis in
stagnant region that does not cause axial displacement.
Therefore, the axial motion of solids in rotary kiln is solely
determined by the axial particle rolling in active layer.
Meanwhile, the randomness of rolling motion will inevi-
tably result in both radial and axial mixing. In this study, it is
assumed that the rolling of particles in the active layer is
induced only by the gravity. Thus, the trajectory of individ-
ual particle during each rolling step follows the direction
determined by the gravitational component vector parallel to
the solid bed surface, as shown in Fig. 1(b). Then the axial
displacement in a single excursion can be calculated accord-
ing to the vector analysis on its trajectory. As the time of a
single excursion is considered, it is valid that the solids’
rolling time is much shorter than their rising time in the
stagnant region provided the active layer is thin, which have
been admitted by Saeman [10] and Gupta and Khakhar [15].
So the rising time of solids in the rotation is nearly equal to
the time of single excursion, which implies the rolling time
shall be ignored.
If the aforementioned PTM is to be further formulated
empirically or simulated numerically, several premises are
required, that is:
1. Steady-state solids flow conditions prevail.
2. The kiln is operated in the rolling mode.
3. The upper surface of solid bed is a plane and the exit end
effect is negligible.
4. Compared to the residence time in stagnant region, the
rolling time on bed surface is negligible (it is precise
enough under low rotating speed).
2.3. Axial displacement in single step by vector analysis
In a single rolling step, the rolling displacement of solids
in the active layer has the axial component and the lateral
one. The relationship between these two components plays
an important role in the development of PTM, which attracts
intensive research efforts [10–12,15,16].
In the Cartesian coordinate system shown in Fig.
1(a,b,c), we denote a, b and d by the kiln slope, the bed
slope and the dynamical angle of repose of solids, respec-
tively. The gravity vector of individual particle can be
expressed as (cosa sin, cosa cos, sina), the normal vector
of bed surface as (0, cosb, �sinb), and the vector of the
symmetric line of bed surface as (0, sinb, cosb). Thus, v, theangle between the gravity and X coordinate, can be
expressed as
cosv ¼ cosasinhd ð1Þ
And g, the angle between the gravity and the symmetric line
of bed surface is expressed as
cosg ¼ cosacoshd sinb þ sinacosb ð2Þ
We define Ds as the rolling distance of a particle in each
step and its components in direction of X coordinate
(namely lateral component) and that in direction of the
symmetric surface line are Dx and Dm, respectively. Defin-
Fig. 1. Schematic view of a single particle trajectory according to PTM starting from gravity-induced rolling. (a) Overall view, (b) simplified gravity analysis,
(c) side view at cross-section, (d) planform of bed surface.
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240230
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ing u as the angle between Ds and Dx, its tangent function is
obtained by dividing Eq. (2) by Eq. (1),
tanu ¼ cosgcosv
¼ cosbtanasinhd
þ cothdtanb
� �ð3Þ
The particle’s axial displacement is given as Dz=Dmcosb.Since tan u=Dm/Dx, the axial displacement in one excursion
can be expressed as
Dz ¼ Dxcos2btanasinhd
þ cothdtanb
� �ð4Þ
Similarly, Saeman [10] and his successors [11–16] have
obtained this relationship all from the simplified geometric
consideration as
Dz ¼ Dxa
sinhdþ bcothd
� �or
Dz ¼ Dxtanasinhd
� cothddh
dz
� �ð5Þ
In Eq. (4), cosb approaches to 1 in the practice, and tan bis just the alternative term of �dh/dx. It indicates that our
relationship from the vector analysis on the gravity-induced
rolling is not only consistent with that of Saeman’s, but also
more reasonable from a point of view of the kinematics of
granular solids.
3. Development of simplified formulas and its validation
We first focus on the development of the simplified
formulas of both MRT and MVF on the basis of PTM.
3.1. Simplified formula of MRT
When lightly loaded kiln (viz. the fill level of solids is
low) is considered, the statistic-averaged method can be
introduced here to derive the formulation of MRT. If the
number of the excursion of solids through whole kiln is
signified as k, the kiln length is equal to
L ¼Xki¼1
Dzi ¼Xki¼1
cos2btanasinhd
þ cothdtanb
� �Dxi ð6Þ
In any specific ist step, the lateral component of rolling
distance, Dxi, is composed of the upper half, xiV, and the
lower half, xiW, of the bed surface (Fig. 1d). Then,
L ¼ cos2btanasinhd
þ cothdtanb
� �Xki¼1
ðxiVþ xiWÞ ð7Þ
One remarkable feature of the rolling mode is that the
position of particle entering into the stagnant region from
the active layer is stochastic because of the rolling step’s
randomicity, meanwhile the position of particle re-entering
the active layer is certain due to the rotation step’s
symmetry. Thus, it is concluded that the lower part of
Dxi in the i step is just the upper part of Dxi+1 in the i+1
step. That is,
xViþ1 ¼ xWi for i ¼ 1; 2: : :k ð8Þ
As was stated earlier, the residence time of one excursion
is mainly determined by the rotation time of solids in the
stagnant region. For the ist excursion, the residence time is
expressed as
ti ¼/r
2pn¼ sin�1ðxiW=rÞ
pnð9Þ
where n is the rotational speed and r the radius of particle
rotation. With respect to low filling ratio of solid bed, Eq.
(9) simplifies to
ti ¼sin�1ðxWi=rÞ
pnc
xWiprn
ð10Þ
So the overall mean residence time through the whole kiln
can be presented as
MRT ¼Xki¼1
ticXki¼1
xWiprn
ð11Þ
Taking Eqs. (7–8) into Eq. (11), we obtain
MRT ¼ Lsinhd2prnðtana þ coshdtanbÞcos2b
þ 1
2prnðxV1 � xWkÞ ð12Þ
where xV1 and xWk are both the random number at age
½0;ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiðR� hÞ2
q� . And the second term in the right of Eq.
(12) is far smaller than the first one and can be ignored if k is
big enough ( > 1000). Then
MRT ¼ Lsinhd2prnðtana þ coshdtanbÞcos2b
ð13Þ
The rotating radius of particle in every excursion is a
random variable related to the rolling distance, Dxi, and the
bed depth, h. Since r is nearly equal to kiln radius R for
lightly filled kiln, R is chosen instead of r as a parameter in
Eq. (13) to predict MRT in practice.
3.2. Simplified formula of MVF
The averaged axial velocity of solids in a single excur-
sion can be expressed by the ratio of L to MRT, then we
get
u ¼ 2prncos2btanasinhd
þ cothdtanb
� �ð14Þ
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240 231
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The increment of area in a cross-section in the ist
excursion can be given as
dA ¼ 2rsin�1 xWir
� �dr ð15Þ
Then multiplying Eq. (14) by Eq. (15) and taking account of
Eq. (10), we get
udA ¼ 2prnð2xWiÞcos2btanasinhd
þ cothdtanb
� �dr ð16Þ
where xWi is given in terms of
xWi ¼ ðr2 � ðR� hÞ2Þ1=2 ð17Þ
The materials flow rate at any axial position can be
expressed as
MVF ¼Z R
R�h
udA
¼ 4
3npcos2b
tanasinhd
þ cothdtanb
� �ð2Rh� h2Þ3=2
ð18ÞFor any rotary kiln operated under steady-state condition,
MVF is uniform at any axial position. However, we find that
the last term in Eq. (18), i.e. (2Rh�h2)3/2, decreases non-
linearly with coordinate Z. Thus, it is concluded that the bed
slope angle b is not a constant along the kiln axis, and the
closer the kiln outlet end is, the larger the slope b is.
Consequently, the approximation of b as mono-value is
very helpful to the application of the empirical formulations,
i.e., Eqs. (13) and (18). Generally, b can be substituted by
the averaged bed slope determined by the difference
between the inlet and outlet depth, that is,
b� ¼ ðh0 � hexÞ=L ð19Þ
In addition, the bed depth (h) in Eq. (18) can be replaced by
the inlet bed depth (h0) in practical cases, since MVF in any
axial point is uniform.
3.3. General formulas with corrected factor
The practical operation of rotary kiln may differ from the
assumptions or ideal cases of PTM, of which the most
common case is the application of internal structures. The
studies of Afacan and Masliyah [20] showed that the
predicting results by PTM have a great discrepancy with
the experimental ones for a case with axial ribs and end
constriction. It is because the mechanism of PTM only
considers the particle–particle interaction in terms of
dynamic angle of repose, but ignores the substantial inter-
action between the particles in the rolling bed and the axial
ribs in the bottom of the drum (Langrish [17]). Thus, the
modification on Eqs. (13) and (18) is inevitable in order to
broaden the validity of our model in such a special case.
Otherwise, the desired rolling mode may be taken place by
the slumping modes for a case with a relatively low rotation.
The loading of system may not always meet the requirement
of the lightly filling of solids. These cases can also result in
the prediction of deviations of PTM, although they are less
appreciable than those arising from internal structures.
Therefore, two correctional coefficients et and ef are intro-
duced in our paper, which can be evaluated by the linear
least-squares fit of experimental and theoretical data. Then
the modified formulas are given as,
MRT ¼ etLsinhd
2pRnðtana þ coshdtanb�Þcos2b�
ð20Þ
MVF ¼ 4ef3
npcos2b� tana
sinhdþ cothdtanb
�� �
� ð2Rh0 � h20Þ3=2 ð21Þ
It seems that et should be the reciprocal of ef from the
derivation of the model. However, it is not the case in fact.
The explanation lies in that the et and ef have other differentcorrecting content besides the joint modification (namely
modification to internal structures, bed modes and bed
slope), e.g., the correction to the substitution of r by R is
considered in et, and that to the replacement of h by h0considered in ef.
3.4. Comparison with experimental results
3.4.1. Cases for the smooth wall without end-constriction
In previous PTM studies, many researchers have adopted
small-size regular materials to verify the validity of the
model [10–13,15]. Here, the importance is attached to the
large-size heterogeneous MSW. Fig. 2 presents the compar-
ison between the experimental and the predicted MRT of
MSW. Reasonable agreement between them is obtained.
The correctional coefficient, et, is about 1.04 and the
correlation factor, R2, is more than 99%. As shown in Fig.
3, similar conclusion on MVF can be drawn. The corre-
Fig. 2. Comparison of MRT by Eq. (20) and experimental one (MSW,
smooth wall).
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240232
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sponding ef and its R2 are about 1.03% and 93.9%, respec-
tively. By the way, Yang’s [22] investigation also showed
that the equation derived from the single particle trajectory
model of Saeman was applicable to predicting MVF of
irregular MSW with very small modification. We tried to
use our Eqs. (20) and (21) to compare with Yang’s exper-
imental data. Similarly the correctional coefficients are
closed to 1, either. Accordingly, it is concluded that the
empirical formulas, Eqs. (20) and (21), can predict both
MRT and MVF quite well for the case of irregular MSW
only with minimum modification, in spite of the different
kiln geometry size.
3.4.2. Cases for internal-structures existence
Figs. 4 and 5 successively show the comparisons
between experimental and predicted results of MRT and
MVF when an internal-structure group labeled 12n–4n is
employed. Although MSWand sand have distinct difference
in the physical or rheological characteristics, their modifi-
cation et as well as ef are quite proximate, which implies that
the influence of internal structure on solid transport is
insensitive to the variation of the feeding materials.
The correctional coefficients of MRT and MVF and their
correlation factors under the various operational conditions
are presented in detail in Table 1. It is noted that the values
of correlation factors more than 90% in all runs reflect the
good linearity between the predicting and measured data,
which further implies the broad applicability of our model to
any special conditions such as internal-structure employ-
ment. When it comes to the industrial-scale rotary kilns, the
current formulas Eqs. (20) and (21) can be precisely applied
as the fundamental to fulfil the optimization of the system,
provided et and ef are regressed by the linear least-squares fit
of a spot of experiments (particularly, et and ef approach one
for an end-opened system).
Moreover, as presented in Table 1, the influences of
internal structures on both MRT and MVF can also be
theoretically explained, which have already been discussed
in part I only from an experimental point of view. For
example, as the height of axial ribs in a certain internal-
structure group increases from 10 to 20 mm (12n–4n!12b–4n), the correctional coefficient for MRT, et, in-
creases only by 3.8–5.0%. As the number of circular ribs
rises from 4 to 7 (12b–4n!12b–7n), the increment of etis 2.4–4.1% for both MSW and sand. However, as height
Fig. 4. Comparison of MRT by Eq. (20) and experimental one (12n–4n
employed).
Fig. 5. Comparison of MVF by Eq. (21) and experimental one (12n–4n
employed).
Table 1
Correctional coefficients et, ef and corresponding correlation factors in
all runs
Case Material et ef
et Correlation
[%]
ef Correlation
[%]
Smooth wall MSW 1.04 99.6 1.03 93.9
12b–4n MSW 1.64 99.0 0.846 98.0
sand 1.67 96.4 0.865 90.1
12b–7n MSW 1.68 93.2 0.771 97.8
sand 1.74 99.6 0.804 98.1
12n–4n MSW 1.58 96.7 0.930 98.4
sand 1.59 97.9 0.905 93.0
12b–4b MSW 1.81 99.2 0.690 97.7
sand 1.83 98.0 0.752 96.3
Fig. 3. Comparison of MVF by Eq. (21) and experimental one (MSW,
smooth wall).
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240 233
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of circular ribs increases from 30 to 50 mm (12b–4n!12b–4b), et increases remarkably by 9.6–10.4%. Thus, it
can be concluded that the effect of the height of circular
ribs is most significant in an internal-structure group. As
far as ef for MVF is concerned, similar conclusion can be
drawn.
4. Development of stochastic PTM and its simulation
So far, we have presented the simplified formulas of
MRT and MVF by using the statistical-averaged analysis
on PTM. But the detailed residence time distribution is
not yet predicted. As mentioned earlier, the most remark-
able feature of PTM is that the position of particle
entering stagnant region from active layer is stochastic
due to the rolling step’s randomicity, while the position of
particle re-entering active layer is certain due to the
rotation step’s symmetry. As for a ternary-mixture system
here, this randomicity should include not only the random
collision of particles (so-called axial mixing), but also the
selectivity of the trajectory of the different particle com-
ponents of mixture (so-called radial and axial segrega-
tion). From studies of Gupta et al. [23], Boateng and Barr
[24] and Bridewater [25], it is doubtless that the trajectory
segregation of particles will play much more important
role in determining the distribution of residence time than
the randomness of particle collision in such a case. So the
randomness of the collision is ignored here in order not to
introduce the excrescent empirical parameter, which had
been considered by Gupta et al. [15] for uniform par-
ticles. The trajectory segregation of different particles
really means the selectivity of the rolling length of
individual particle in the active layer. Thus, if the prob-
ability distribution function of the end point of rolling
distance (e.g., xiW, see Fig. 1) is given, a random PTM
can be extended to predict RTD curves.
4.1. Calculation of single particle’s residence time
In this paper, the stochastic PTM was developed as a
computer program, see Fig. 6 for the Flow-sheet. The
main idea of random PTM is to introduce the certain
number of tracers into a steady-state rotary kiln, calculate
the residence time of individual tracer one by one and
conduct the statistic analysis on the distribution of all
tracers. The calculation of the residence time of individual
particle plays an important role, which consists of five
main procedures defined as initialization of the particle
position at kiln inlet, judgement of the upper half loca-
tion, selection of probability distribution of rolling dis-
tance, rolling step calculation and rotation step calculation,
respectively.
In our program (Fig. 6), as a tracer enters a steady-
state kiln, its initial axial position (z) as well as radial
position ( y) are a certain value, and they are equal to zero
and R�h0, respectively. However, the initial lateral loca-
tion is a random value, which is given as,
xV¼ x0 unifrndð�1; 1Þ ð22Þ
where x0 is the half length of active layer surface, and
unifrnd (�1, 1) is a uniform random number in the range
(�1, 1). Subsequently, we shall judge whether the initial
location of tracer is on the upper half of bed surface.
Once the tracer locates at the lower half surface, a
rotation step will conduct and the residence time of the
tracer begins to be accumulated according to Eq. (9), and
then particle will arrives to its symmetrical position at the
upper half surface.
Then the tracer will roll on the active layer. The
determination of the end-point of rolling step (i.e., the
position that tracer enters stagnant region from active layer,
xW) is a key element for developing the random PTM.
According to previous studies, xW shall be a random number
subjected to a specified distribution. In order to find the
valid probability distribution for xW, the effect of segregationof materials used must be considered, which is discussed it
in detail as follows.
4.1.1. Probability distribution for xW with ideal materials
If materials used are ideal homogeneous particles of the
same type, size and rheological property, there is no
segregation in kiln. The probability distribution for xW is
easily obtained by considering the volumetric fraction of
particles that enter the stagnant region from the active layer
in the range (xW, xW+dxW) at a particular axial position (see
Fig. 7). As the kiln rotates an angle interval, y/r, we have
pðxW; xWþ dxWÞ ¼ x0dxWdzy/r
ðx20=2Þdzy/r
¼ 2xW
x0
� �d
xW
x0
� �ð23Þ
where the half length of active layer x0 changes with respect
to coordinate z. It is apparent that the probability for xW/x0 isa specified term of Beta(a,b) distribution with factors a=1
and b=2 (Gupta and Khakhar [15]). Thus, xW can be
obtained by,
xW ¼ x0Betarnd ð2; 1Þ ð24Þ
where Betarnd (2,1) is a random number subjected to Beta
(2,1) distribution.
4.1.2. Probability distribution for xW with segregated mate-
rials
For the most general cases, materials used have different
sizes or types, especially for the case of MSW pyrolyser/
incinerator. Therefore, the effect of the segregation on
probability distribution for xW should be considered. See
Fig. 8, Boateng and Barr [24] proposed that the radial
segregation of materials tends to concentrate finer particles
within the core and hence cause the trajectory segregation of
different sized particle. That is, the smaller particles will
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Fig. 6. Flow-sheet of numerical simulation of RTD by stochastic PTM.
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240 235
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enter stagnant region with the smaller xW (namely the end of
rolling distance), while larger ones will enter with the large
xW. Due to segregation, xW is dispersed around a point x�Wwith a variance r0 that decreases with an increasing segre-
gation level of MSW. Because of the lack of a predictive
model about relations between the segregation with the
variation of particle properties, we assume that x�W is
symmetric to the particle start point of rolling, xV. So in
our model different xV correspond to particles with different
flow properties. Thus, It can be inferred that the term of
(xW�xV)/r0 can be described as a random number subjected
to a truncated standard Gaussian distribution. The Gaussian
distribution is truncated in order to limit xW in the range
(0,x0). Normalizing variance r0 as rs with respect to x0, then
xW can be obtained as,
xW ¼ xVþ rsx0 Normrndð0; 1Þ að0; x0Þ ð25Þ
where Normrnd(0,1) is a random number subjected to
standard Gaussian distribution.
As long as the start and end of rolling distance, xV and
xW, is formulated, the value of rolling distance can be
determined by Dx=xV+xW. Then the calculation of rolling
step is conducted, in which the axial displacement z of a
particle is obtained by Eq. (4). One advantage of the
model presented here over the previous ones (e.g., Kohav
et al. and Gupta et al.) is that the varied bed depth profile
(i.e., the bed slope) is incorporated into random PTM.
That is, the fill level of solids along kiln axis varies, which
leads to the variation of the trajectory of particles at
different cross-section. According to previous studies on
bed depth profile (Kramers and Croockewit [12] and
Lebas et al. [18]), the bed slope is given in terms of a
differential equation,
tanb ¼ dh
dx¼ tana
coshd� 3MVFtanhd
4pnR3
2h
R� h
R
� �2" #�1:5
ð26Þ
As the fill level of solids is low (e.g., h0/R<0.5), the
formula can be altered by,
tanb ¼ dh
dx¼ h0 � hex
Lð27Þ
As bed slope is solved by above formulas, the particle’s
coordinate y and the half length of active layer x0 at
different axial position z can be accounted for, as given in
Flow-sheet by Fig. 6.
Finally, the calculation of rotation step is conducted, in
which the residence time of single tracer is acquired by
accumulation of Eq. (9). It is noted that only the time during
rotation step is accumulated while the time during rolling
step is ignored in our work, the feasibility of which has
already been proved by other researchers [10,15,16]. After
rotation step, the tracer will reach the symmetric point of xW,namely xV=xW. So far, the tracer completes an intact excur-
sion. Again a new rolling step occurs, so does a new rotation
step. The procedure is repeated until the tracer exits the kiln
(z>L). In common case, the residence time of a tracer
through whole kiln can be gained after experiencing about
more than 1000 excursions.
4.2. Statistic analyses on RTDs
The residence time of each tracer is calculated by
aforementioned method and registered as ti. Denoting the
number of tracers introduced by N, the mean residence time
and relative variance is defined as,
MRT ¼ 1
N
XNi¼1
ti ð28Þ
rr2 ¼ 1
N � 1
XNi¼1
ðti �MRTÞ2=MRT2 ð29Þ
Thus, the detailed RTD curve can be fitted by,
f ðtÞ ¼ 1ffiffiffiffiffiffi2p
prrMRT
exp � ðt=MRT� 1Þ2
2rr2
!ð30Þ
As soon as RTD of solids is determined by numerical
simulation, the dispersion coefficient in terms of Peclet
Fig. 7. Schematic of volumetric fraction of particles entering stagnant
region at xW.
Fig. 8. Schematic of radial segregation of particles within a cross-section
of kiln.
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number, namely the ratio of convection to diffusion times,
can be evaluated by the relative variance rr,
rr2 ¼ 2
Pe� 2
Pe2½1� expð�PeÞ� ð31Þ
And for large Pe (>100), the approximation
Pe ¼ 2
rr2
ð32Þ
is applicable. The equation above indicates that rr can
take place of Pe to evaluate the axial dispersion of solids
in kiln.
4.3. Simulation results
Numerical simulation was carried out to determine
detailed RTDs as well as s and rr of RTDs. In most practical
rotary-kiln reactors such as waste incinerator/pyrolyser, the
kiln is usually operated with a slight inclination from the
horizontal and its outlet end is open without dam. In such
case, both the kiln slope and bed slope should be taken into
accounted in stochastic PTM. However, so far the research on
PTM considering both these two aspects simultaneously is
absent. In our simulations, the kiln outlet is open for all runs
(hex/R=0), which implies the bed slope can not be ignored. In
addition, unless otherwise stated, we set L/D=6, a=2.40, n=4rpm and d=48.5j for all runs, among which the last one is in
accordance with the dynamic angle of repose of MSW.
The simulated RTD densities of ideal particles and
segregated particles, as well as the normal distribution fit
curves, are illustrated in Fig. 9. It can be seen that the RTD
of ideal particles is well fitted by the normal distribution
density function with a low relative variance (rr=0.0075).As it comes to the segregated particles, the trajectory
segregation in terms of the variance of rolling distance
(rs) due to variation in particle flow properties will deter-
mine the residence time distribution. The reduction of rs
(namely the increment of radial segregation of solids)
causes not only the great increment of rr of RTD, but also
increasing discrepancy of the solid’s RTD with the normal
distribution fit curve. That is, as rs varies from 0.5 to 0.1,
rr increases by more than 200% while MRT increases by
less than 1%. It is inferred that the solids’ segregation in
kiln has effect on rr but not on MRT. Moreover, the
simulated RTD for the case of rs=0.1 has a relative great
discrepancy with the normal distribution fit curve, as shown
in Fig. 9.
In order to verify the validity of our stochastic PTM for
segregated MSW, the comparison between the numerical
simulation and the experiment is performed. In this simu-
lation, the segregation factor, rs, is regressed as 0.1 by the
linear least-squares fit between experimental rr and simu-
lated rr of RTD. In addition, the results of MRT calculated
by simplified Eq. (20) are also attached. As shown in Fig.
10, the simulated MRT from stochastic PTM agrees quite
well with the experimental one, while the simplified Eq.
(20) predicts a slightly shorter MRT than experiments. It is
because that the simplified Eq. (20) is developed under the
premise of the lightly loaded kiln. Fig. 11 shows the
comparison between experimental and simulated rr or r.The reasonable agreement is reached, especially taking
account of the high measuring error of rr or r due to the
high MSW segregation.
Fig. 9. Residence time distribution obtained from stochastic PTM (a=2.40j;n=4 rpm; h0/R=0.5; hex/R=0; hd=48.5).
Fig. 10. MRT from both PTM and experiments with various rotation
speed.
Fig. 11. Variance from both stochastic PTM and experiments with various
rotation speed.
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To further discuss the predicted difference of MRT
between stochastic PTM and simplified Eq. (20), the sim-
ulations under various inlet bed depths are conducted. Fig.
12 shows the comparison between MRT obtained from
various segregated stochastic PTM and that obtained from
simplified Eq. (20). For all models, MRT decreases with the
increment of the inlet bed depth (h0/R). It can be explained
that the increasing h0/R causes the increment of bed slope
(here, kiln outlet keeps open, hex/R=0), and thus the incre-
ment of axial displacement in a single step (see Eq. (4)),
which finally results in the reduction of residence time.
Moreover, the simplified Eq. (20), developed for lightly
loaded kilns, predicts shorter MRT than all stochastic PTM.
The higher the value of h0/R is, the greater the difference
between them is. The high h0/R implies the high fill level of
solids in kiln. Therefore, the simplified Eq. (20), assuming
the kiln to be lightly loaded, will differ greatly from the
stochastic PTM under the case of high h0/R. The conclusion
is drawn again that the solid’s segregation does not influ-
ence MRT apparently, though it exerts a great influence on
the dispersion of RTD (shown in Fig. 13). As rs varies from
0.7 to 0.1, rr increases from 40% to 280%. Furthermore, the
higher the value of h0/R is, the higher increasing rate of rr is
and the more violent dispersion of RTD prevails.
5. Appliance of PTM in optimization
5.1. Optimizing model development
According to simplified Eqs. (20) and (21), the optimiz-
ing geometry design model of rotary kiln pyrolyser can be
developed. The object function of the optimization is the
minimal space occupied or the minimal consumption of
steel. The constraints are imposed by the practical operating
variables (rotational speed and kiln slope), the permits of
desired MVF, the permit of the complete pyrolysis time, the
design of the kiln (exit dam and internal structures), the
limits of heat transfer, and the experiential limitation of L/R
of the kiln. Concretely, the fill ratio of solids in kiln is
generally less than 20% in order to keep the high efficient
heat transfer or energy utilization [26]. The complete
pyrolysis time is about 45–60 min by experiences, which
shall be less than MRT [27]. The ratio of the outlet to inlet
depth, hex/h0, replaces the average bed slope, b�, in the
optimization model. Then the optimizing geometry design
model of rotary kiln is described as,
min p R2 L
s:t: MVFðR; L; a; n; h0; hex=h0Þ ¼ fre
MRTðR; L; a; n; h0; h0=hexÞ ztre
alVaVau
nlVnVnu
Cðh0;RÞV0:2
hex=h0V1
8VL=RV12
9>>>>>>>>>>>>>>=>>>>>>>>>>>>>>;
ð33Þ
where C represents the fill ratio at inlet end and is expressed
in terms of h0 and R,
C ¼ 1
pcos�1 R� h0
R
� �� ðR� h0Þ
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið2Rh0 � h20Þ
ppR2
ð34Þ
In Eqs. (33) and (34), the dimensions of MVF, MRT and n
are l/min, min and rpm, respectively. And the international
Fig. 12. MRT obtained from stochastic PTM and empirical formula with
various inlet bed depths.
Fig. 13. rr obtained from random PTM with various inlet bed depths.
Table 2
Optimal solution to the scale design of rotary kiln to dispose solid waste
with various tre (MVF=0.5 l/min)
MRT
(tre)
[min]
n [rpm] a [rad] h0 [m] hex/h0 C L [m] D [m] H
20 1.000 0.0300 0.0741 0.5000 0.2 1.8006 0.2917 0.14
25 1.0000 0.0285 0.0719 0.4221 0.2 1.4206 0.2828 0.14
30 1.0002 0.0300 0.0728 0.4435 0.2 1.6626 0.2864 0.14
35 1.0000 0.0277 0.0753 0.5000 0.2 1.8091 0.2965 0.14
40 1.0039 0.0109 0.0853 0.4961 0.2 1.6132 0.3357 0.14
45 1.0000 0.0106 0.0869 0.5000 0.2 1.7494 0.3419 0.14
50 1.0000 0.0100 0.0885 0.5000 0.2 1.8738 0.3483 0.14
55 1.0000 0.0100 0.0895 0.5000 0.2 2.0125 0.3524 0.14
60 1.0000 0.0100 0.0905 0.5000 0.2 2.1488 0.3563 0.14
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240238
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standards are adopted for the rest. The upper and lower
limits of a are 0.01 and 0.03, respectively. The rotating
speed is limited from 0.5 to 8 rpm.
5.2. Discussions on the solution of optimization
Eq. (33) is a single-objective, constrained and nonlinear
optimization problem. Subsequent quadratic program (SQP)
in Matlab Toolbox can be employed to solve it [28]. The
optimum geometry design of rotary kiln pyrolyser can be
considered starting from two aspects. On one hand, MSW is
generally composed of various components such as woods,
plastics and papers, each of which has a different tre. When
MVF is given as 0.5 l/min, the optimum solution to the
geometry design of rotary kiln with various tre is presented
in Table 2. On the other hand, rotary kiln is sometimes used
to pyrolyze the unitary wastes such as scrap tyre, which has
the common tre. So the optimum solution to the design of
rotary kiln under varied MVF is presented in Table 3.
From above Tables, it can be seen that the fractional
hold-up (i.e. overall fill ratio) in terms of H=MRT�MVF/VR
keeps as a constant about 0.14 during the optimization (this
value is also calculated as 0.143 by Hehl et al.’s empirical
formula [14]). Thus it is concluded: (1) the reactor volume is
only dependent to the products of MRT and MVF for a
given inlet G(h0,R); (2) a, n and L/D are just the flexible
adjustable parameters to meet the required MRT or MVF.
The conclusion is absolutely much meaningful to the scale-
up of rotary kiln. By the way, we have already designed and
built a technical-scale rotary kiln pyrolyser of waste tyre on
the basis of above results, which is given in detail in
literature [29].
6. Conclusion
The vector analysis is originally adopted to account for
the gravity-induced axial displacement in a single rolling
step, which promotes the physical basis of PTM pioneered
by Saeman. Then, three parts of work based on the PTM are
extended intensively, as follows.
(1) The statistical-averaged analysis on PTM is intro-
duced for lightly filled kiln. The simplified formulas on both
MRT and MVF are deduced, which are presented as Eqs.
(20) and (21), respectively. Two correctional, factors et andef, are proposed to improve model validity under practical
conditions such as internal-structure presence. Good agree-
ment is obtained between the empirical formulas and experi-
ments with correlation factor in excess of 90% in all runs.
(2) A stochastic PTM incorporating the trajectory segre-
gation of MSW (rs) is developed originally to predict
detailed RTD curves in an inclined rotary kiln, in which
bed depth varies. The main cause of the dispersion of RTD
is the segregation of particle rolling distance in a single
excursion, due to variation of MSW flow properties. As rs
changes from 0.5 to 0.1, rr increases by more than 200%
while MRT varies by less than 1%. The simulated RTD
from stochastic PTM fits quite well with the experimental
one, while the simplified Eq. (20) predicts a slightly shorter
MRT than experiments. The predicted difference between
stochastic PTM and simplified equation is related to the fill
level of solids, namely the bed inlet depth h0/R for an end-
opened system.
(3) The optimizing models for the geometry design of a
laboratory-scale rotary kiln pyrolyser are proposed and the
optimal solutions are discussed in this work. These results
have given author many useful references in the design and
development of a technical-scale rotary kiln pyrolyser of
waste tyre.
Acknowledgements
This research was supported mainly by Nation Natural
Science Funds of China (No. 50076037) and partially by
Zhejiang Provincial National Science Funds of China (No.
RC99041). We are grateful to Dr. A.-M. Li for helpful
discussions about rotary kiln transport processes. The
contributions of Dr. J.T. Huang and Z.X. Zhang to this
work is gratefully acknowledged.
References
[1] H. Henein, J.K. Brimacombe, A.P. Watkinson, Experimental study of
transverse bed motion in rotary kilns, Metall. Trans. B 14B (1983)
191–204.
[2] P.V. Danckwerts, Continuous flow systems—distribution of residence
times, Chem. Eng. Sci. 2 (1953) 1.
[3] L.T. Fan, Y.K. Ahn, Axial dispersion of solids in rotary solid flow
systems, Appl. Sci. Res. A10 (1961) 465.
[4] R. Rutgers, Longitudinal mixing of granular material flowing through
a rotary cylinder—Part I. Descriptive and theoretical, Chem. Eng. Sci.
20 (1965) 1079–1087.
[5] A.Z.M. Abouzeid, D.W. Fuerstenau, A study of the hold-up in rotary
drums with discharge end constrictions, Powder Technol. 25 (1980)
21–29.
[6] G.W.J. Wes, A.A.H. Drinkenburg, S. Stemerding, Solids mixing and
residence time distribution in a horizontal rotary drum reactor, Powder
Technol. 13 (1976) 177–184.
[7] J. Mu, D.D. Perlmutter, The mixing of granular solids in a rotary
cylinder, AIChE J. 26 (6) (1980) 928.
[8] P.S.T. Sai, G.D. Surender, A.D. Damodaran, V. Suresh, Z.G. Philip,
Table 3
Optimal solution to the scale design of rotary kiln with various MVF under
condition of the same tre (MRT or tre=45 min)
MVF
[l/min]
n [rpm] a [rad] h0 [m] hex/h0 C L [m] D [m] H
0.2 1.0049 0.0292 0.0560 0.4995 0.2 1.6843 0.2204 0.14
0.3 1.0020 0.0239 0.0665 0.4987 0.2 1.7938 0.2616 0.14
0.4 1.0177 0.0135 0.0783 0.4837 0.2 1.7227 0.3082 0.14
0.5 1.0000 0.0106 0.0869 0.5000 0.2 1.7494 0.3419 0.14
0.6 1.0000 0.0100 0.0928 0.5000 0.2 1.8407 0.3652 0.14
0.7 1.0000 0.0100 0.0976 0.4998 0.2 1.9394 0.3843 0.14
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240 239
中国科技论文在线______________________________________________________________________________________www.paper.edu.cn
K. Sankaran, Residence time distribution and material flow studies in
a rotary kiln, Metall. Trans. B 21B (1990) 1005–1011.
[9] G. Groen, J. Ferment, M.J. Grorneveld, J. Decleer, A. Delva, Scaling
down of the calcination process for industrial catalyst manufacturing,
Proc. Int. Symp. Sci. Basis for the Preparation of Heterogeneous
Catalysts, Elsevier, Amsterdam, 1986.
[10] W.C. Saeman, Passage of solids through rotary kilns—factors affect-
ing time of passage, Chem. Eng. Prog. 47 (10) (1951) 508.
[11] L. Vahl, W.G. Kigma, Transport of solids through horizontal rotary
cylinders, Chem. Eng. Sci. 1 (1952) 253.
[12] H. Kramers, P. Croockewit, The passage of granular solids through
inclined rotary kilns, Chem. Eng. Sci. 1 (1952) 258–265.
[13] R. Rogers, P.P. Gardner, A Monte Carlo method for simulating dis-
persion and transport through horizontal rotating cylinder, Powder
Technol. 23 (1979) 159–167.
[14] M. Hehl, H. Kroger, H. Helmrich, K. Schugerl, Longitudinal mixing
in horizontal rotary drum reactors, Powder Technol. 20 (1978) 29.
[15] S.D. Gupta, D.V. Khakhar, Axial transport of granular solids in hor-
izontal rotating cylinders: Part 1. Theory, Powder Technol. 67 (1991)
145–151.
[16] T. Kohav, J.T. Richardson, D. Luss, Axial dispersion of solid particles
in a continuous rotary kiln, AIChE J. 41 (1995) 2465–2475.
[17] T.A.G. Langrish, The assessment of a model for particle transport in
the absence of airflow through cascading rotary dryers, Powder Tech-
nol. 74 (1993) 61–65.
[18] E. Lebas, F. Hanrot, D. Abilitzer, J.L. Houzelot, Experimental study of
residence time, particle movement and bed depth profile in rotary
kilns, Can. J. Chem. Eng. 73 (1995) 173–179.
[19] R.J. Spurling, J.F. Davidson, D.M. Scott, The no-flow problem for
granular material in rotating kilns and dish granulators, Chem. Eng.
Sci. 55 (2000) 2303–2313.
[20] A. Afacan, J.H. Masliyah, Solid hold-up in rotary drums, Powder
Technol. 61 (1990) 179–184.
[21] C. Wightman, M. Moakhar, F.J. Muzzio, O. Walton, Simulation of
flow and mixing of particles in a rotating and rocking cylinder, AIChE
J. 44 (1998) 1266–1276.
[22] W.-C. Yang, Dynamics of simulated municipal solid waste in a rotat-
ing device, Powder Technol. 72 (1992) 139–147.
[23] S.D. Gupta, D.V. Khakhar, S.K. Bhatia, Axial segregation of particles
in a horizontal rotating cylinder, Chem. Eng. Sci. 46 (1991) 1517.
[24] A.A. Boateng, P.V. Barr, Modelling of particle mixing and segregation
in the transverse plane of rotary kiln, Chem. Eng. Sci. 51 (1996)
4167–4181.
[25] J. Bridewater, Particle mixing and segregation in failure zones—
theory and experiment, Powder Technol. 41 (1985) 147–158.
[26] R. Calvin, P.E. Brunner, Handbook of Hazardous Waste Incineration,
TAB Books, USA, 1989.
[27] A.M. Li, X.D. Li, S.Q. Li, Pyrolysis of solid waste in a rotary kiln:
influence of final pyrolysis temperature on pyrolysis products, J. Anal.
Appl. Pyrolysis 50 (1999) 149–162.
[28] G.V. Reklaitis, A. Ravindran, K.M. Ragsdell, Engineering Optimiza-
tion, Methods and Applications, Wiley, New York, 1983.
[29] Y. Chi, S.-Q. Li, J.-T. Huang, Clean fuels from pyrolysis of scrap tyre
in rotary kiln: experimental studies and mechanical design, 3rd Inter-
national Symposium on Incineration and Flue Gas Treatment Tech-
nology, Incineration Division, Section 7, Brussels, July, 2001.
S.-Q. Li et al. / Powder Technology 126 (2002) 228–240240
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