Chemical Engineering Communications
ISSN: 0098-6445 (Print) 1563-5201 (Online) Journal homepage: http://www.tandfonline.com/loi/gcec20
Continuous Dosing of Fast Initiator during
Suspension Polymerization of Vinyl Chloride for
Enhanced Productivity; Mathematical Modeling
and Experimental Study
Mohammad Javad Bijhanmanesh, Nasrin Etesami & Mohsen Nasr Esfahany
To cite this article: Mohammad Javad Bijhanmanesh, Nasrin Etesami & Mohsen Nasr Esfahany
(2016): Continuous Dosing of Fast Initiator during Suspension Polymerization of Vinyl Chloride
for Enhanced Productivity; Mathematical Modeling and Experimental Study, Chemical
Engineering Communications, DOI: 10.1080/00986445.2016.1205981
To link to this article: http://dx.doi.org/10.1080/00986445.2016.1205981
Accepted author version posted online: 05
Jul 2016.
Published online: 05 Jul 2016.
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Date: 07 July 2016, At: 03:50
Continuous Dosing of fast Initiator during Suspension Polymerization of Vinyl
Chloride for Enhanced Productivity; Mathematical Modeling and Experimental
study
Mohammad Javad Bijhanmanesh1, Nasrin Etesami1, Mohsen Nasr Esfahany1
1
Department of Chemical Engineering, Isfahan University of Technology, Isfahan, Iran
E-mail: netesami@cc.iut.ac.ir
Abstract
Chemical Engineering Communications
An adopted mathematical model was developed to reduce the batch time required for the
suspension polymerization of vinyl chloride in order to improve productivity by
continuous dosage of a fast initiator during polymerization reaction. The model was
accompanied by a particle swarm optimization (PSO) algorithm so as to optimize the
initiator dosage rate during the process for a certain conversion. A pilot scale reactor was
employed to verify the mathematical model predictions. This showed that the model
predictions are in very good agreement with the experimental data. A proper initiator
dosage trajectory during the course of the reaction was obtained in such a way that the
reaction rate over the course of polymerization was constant and corresponded to the
maximum rate in the conventional case (non-continuous addition of a mild initiator). The
maximum reduction in reaction time relative to conventional polymerization for the
predefined conversion was 53%. Analyzing the molecular characteristics of the samples
showed that the molecular characteristics of the final PVC product remained relatively
unchanged under an optimum initiator dosage trajectory compared with the conventional
process.
1
KEYWORDS: PVC, Suspension polymerization, Mathematical modeling, Optimization,
Fast initiator, Continuous dosage
INTRODUCTION
Poly (vinyl chloride) (PVC) is a versatile plastic which is often produced through the
suspension polymerization technique. The VCM suspension polymerization is typically
carried out in an isothermal batch-wise process (Saeki and Emura, 2002). The monomer
is initially dispersed in droplet form in the size range of 50–500 μm using the combined
Chemical Engineering Communications
action of agitation and surface active agents. In the conventional process for VCM
polymerization, the initiator is entirely added to the reactor at the beginning of the
reaction. Polymerization begins by decomposing monomer-soluble initiators in the
droplets at reaction temperature converting the liquid droplets into rigid, porous polymer
particles (Feldman et al., 1977). In such polymerization systems, an auto-acceleration of
the reaction rate occurs. The maximum cooling capacity of the reactor corresponds with
the maximum rate of the heat release at the exothermic peak (Pinto and Giudici, 2001). In
this case, the full capacity of the cooling system remains unutilized most of the time
during the course of the polymerization, particularly at the beginning of the reaction. The
activity of the initiator and the polymerization temperature are strategic factors that can
be manipulated to control the rate at its maximum constant value, and hence to reduce the
batch time of the polymerization reaction (Darvishi et al., 2015; Feldman et al., 1977;
Meulenbrugge et al., 2007; Pinto, 1990; Pinto and Giudici, 2001; Van Swieten et al.,
2002, 2003; Westmijze et al., 2012; Westmijze et al., 2013). The ways of implementing
these strategies involve applying a temperature program, a cocktail of initiators and an
2
initiator dosage system in such a way that the polymerization rate is kept constant at the
desired value.
Achieving the constant maximum reaction rate and hence using from the full capacity of
the cooling system during the polymerization time is possible by means of continuous
dosing of a fast initiator during the polymerization reaction. The continuous initiator
dosage allows for the spreading of heat the reaction over the course of the time during
which polymerization occurs, which allows for a higher degree of control of the
Chemical Engineering Communications
polymerization rate.
This process was found to solve a number of drawbacks which originate when using mild
initiators, such as poor initiator efficiency and high residual initiator levels in the resin
produced. Akzo Nobel Company (Netherlands) suggested a process in which initiators
having a half-life in the range of 0.0001-1.0 hour at the polymerization temperature are
dosed to the reaction mixture so as to improve productivity (Teiji et al., 1986; Van
Swieten et al., 2002, 2003; Westmijze et al., 2012; Westmijze et al., 2013). However, the
study did not consider how to optimize the rate of initiator dosage as well as the effects
on the properties of the final product.
However, because of the time consuming nature of the batch polymerization of PVC, the
determination of an optimal initiator dosing regimen for the best enhanced productivity is
very difficult to establish experimentally. Therefore, the use of modeling and simulation
to obtain an optimal initiator dosing rate is ineviTable . Up to the present, various
3
mathematical models have been developed for regular polymerization process of VCM,
but no such models have yet been adopted for a continuous initiator dosage system
(Alexopoulos and Kiparissides, 2007; Kiparissides et al., 1997; Krallis and Kiparissides,
2007; Olaj, 1977; Suresh and Chanda, 1982; Ugelstad, 1977; Xie et al., 1991a).
In this paper, a mathematical model for the suspension polymerization of VCM with
continuous dosages of initiator is developed in which adjusTable parameters are specified
using experimental data. The model is then optimized using a PSO algorithm (Eberhart
Chemical Engineering Communications
and Kennedy, 1995) to achieve an optimal dosing trajectory of the fast initiator with a
predefined reaction rate and VCM conversion. The model is validated against the
experimental data obtained from performing the suspension polymerization experiments
in the pilot-scale reactor. The effect of a continuous dosage initiator on polymerization
time and molecular characteristics of the final PVC resin (MW, K value and MWD) are
also investigated using several simulation runs.
MATERIALS AND METHODS
Model Development
Our simulations rely on a mathematical model which is a combination of the models
provided by Xie, et al., and Kiparissides, et al., in which the polymerization reaction was
considered in both monomer and polymer phases (Kiparissides et al., 1997; Xie et al.,
1991a). Accordingly, the two-phase based reaction rate can be expressed by differential
equations as follows:
4
dX 1
K p1M1 R 1 K p 2 M 2 R 2
dt M 0
(1)
where, Mo is the initial mass of VCM (g), Kp, M and [R•] are the propagation rate constant
(l mol-1 s-1), the masses of monomer (g) and the radical concentrations in the monomer
and polymer phases (mol l-1), respectively. In the current study, subscripts 1 and 2
represent the monomer and the polymer phase, respectively.
Given that free-radical polymerization of VCM is accompanied by some physical
Chemical Engineering Communications
transitions which influence the reaction phases, the model divides the course of
polymerization into three stages. During the first stage, conversion is very low (X<0.001)
and there is no separate polymer phase as yet, the reaction occurs merely in monomer
phase. Monomer mass distributions in two phases will be given by:
M1 M 0 (1 X ) M g M w ; M 2 0.0
(2)
where Mg and Mw are the masses of monomer in gaseous and aqueous phases and will be
expressed by (Xie et al., 1991a):
XM 0 1/ Dm 1/ Dp
MWm Pm0
Mg
(1 W1 )Vr
RT
1 Dg 0 / Dm
M w KWw
(3)
(4)
where, MWm is the monomer molecular weight (g mol-1), Pm0 is the saturation pressure of
the monomer (atm), W1 is the initial fillage factor of reactor, Vr is the reactor volume (l),
Dm, Dp and Dgo are the densities of monomer, polymer and monomer vapor (g l-1), K is
the monomer solubility constant in water at polymerization temperature
5
( K 0.0472 11.6 / T ) and Ww is the water mass in the continuous phase (g). The
reaction rate equation for the first stage, therefore, becomes (Xie et al., 1991a);
dX 1 K p1
1/2 M1 RI 1
dt M 0 Kt1
X 0.001
(5)
where, Kt and RI are termination rate constant (l mol-1 s-1) and initiation rate (mol l-1 s-1).
The second stage starts with X>0.001 to the critical conversion (Xf) at which the pressure
in the reactor started to drop due to monomer starvation. During this stage, the polymer
Chemical Engineering Communications
phase appears and the polymerization reaction continues in both the polymer and the
monomer phases at different rates. During this stage, the transfer of VCM from the
monomer to the polymer phase takes place continually, so that the polymer phase will be
evenly saturated with monomer. The following equations can be written for monomer
mass distribution in each phase as (Kiparissides et al., 1997; Xie et al., 1991a):
M1 M 0 (1 X ) M g M w M 2
M2
X
M 0 (1 X f ) M gXf M w
Xf
(6)
(7)
where MgXf is the mass of monomer in gaseous form at Xf and Xf given by (Kiparissides et
al., 1997; Xie et al., 1987):
Xf
M 0 Dg 0 (1 W1 )Vr KWw
1
1
(
)
D
g
0
D (1 ) D
Dp
2
M 0 1 m
m
Dg 0
2 D p
1
Dm
6
(8)
where, φ2 is the volume fraction of polymer in polymer-rich phase. φ2 is related to the
ratio of the partial pressure of VCM (Pm) to its saturated value (Pm0) at the reactor
temperature and can be obtained by Flory-Huggins equation (Kiparissides et al., 1997;
Xie et al., 1991a):
P
ln m ln 1 2 2 22
Pm0
(9)
where χ is VCM-PVC interaction parameter at polymerization temperature (T) that will
Chemical Engineering Communications
be given by (Xie et al., 1991a):
1286.4
3.02
T
(10)
A separate monomer phase is available (in the second stage), and the polymer-rich phase
remains thermodynamically in equilibrium with monomer. Therefore, the monomer
vapor pressure will be equal to its saturated value, (Pm=Pm0).
The reaction rate for the second stage can be expressed by (Xie et al., 1991a):
dX 1 K P1
( J12 4Kt1 J 2 J1 )M1
dt M 0 2Kt1
V
J1 1 ( J12 4Kt1 J 2 J1 )
K
V
V2
M 2
P12 R12 (1 Kde ) K RI 1 1
2 Kt 1
V2
Kt22
(11)
0.001 X Xf
where, V1 and V2 are the volumes of monomer and polymer phases in the reaction,
'
respectively, Kde is the desorption rate constant of radicals from polymer phase (s-1),
K is a precipitation constant for polymer radicals and J1 and J2 are defined parameters in
7
Xie’s model, depending on desorption and precipitation rate of radicals from/into
polymer phase (Xie et al., 1991a).
The third stage is related to the conversions higher than Xf (Xf<X <1.0) in which the
monomer completely disappears as a separate phase and as a monomer-swollen polymer
phase. After this point, the polymerization will proceed in the polymer phase under
diffusion-control reactions (at initiation, termination, and propagation steps) which were
modeled with a free volume approximation. Monomer mass weight in each phase, and
Chemical Engineering Communications
the reaction rate for the third stage, will be given by (Kiparissides et al., 1997; Xie et al.,
1991a):
M1 0.0; M 2 M 0 (1 X ) M g M w
Mg
(12)
1
Dg 0
1
MWm Pm
X
X
(1 W1 )Vr M 0
f
RT
Dm Dg 0
Dm Dp
dX 1 K p 2
M
R
2
2
I
1/2
dt M 0 Kt 2
(13)
XXf
(14)
The total rate of initiator decomposition can be expressed by (Kiparissides et al., 1997;
Xie et al., 1991a):
d[ I ]
2 f kd I
dt
(15)
where, f, kd and [I] are the efficiency, initiation rate constant and concentration of the
initiator.
8
In the method of continuous dosing of initiator during polymerization process, the mole
of the fast initiator at each time step (in numerical solution of the discretized equations) is
also calculated using the following equation:
t
I t I add
I t t exp(kd t )
(16)
where, ∆t represents the time step size in numerical solution and
t
I add
is the mole of
initiator dosed up at each time step. It is obvious that in a conventional polymerization
system in which the initiator is entirely added to the reactor at the beginning of the
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process, the value of
t
I add
will be zero.
Since dosing the initiator during the course of the polymerization causes the initiator
[ I ]2
partition coefficient (K = [ I ]1 ) to vary, it is taken as an adjusTable parameter in the
I
kinetic model which is derived from appropriate experimental data.
The number and weight averaged molecular weight ( M n and M w ) are calculated using
moment methods. The ith moments for the dead and live polymer distribution Qi and Yi
are defined as (Kiparissides et al., 1997; Xie et al., 1991b):
Qi r 1 r i Pr
(17)
Yi r 1 r i Rr
(18)
where, r is the chain length, Pr and Rr are the concentration of live and dead
macromolecules with chain length of r, respectively. The remainder of polymerization
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kinetic equations and molecular weight are used to calculate the average molecular
weight and molecular weight distribution are the same as those provided by Xie, et al.
(Xie et al., 1991b).
Fikentscher's K-values as a molecular characteristic (Fikentscher, 1932) can be evaluated
by solving the equation which is related to relative viscosity (ηrel) according to:
75K 2 106
log(rel )
K 103 C
3
1 1.5 C K 10
(19)
Chemical Engineering Communications
where, C is the concentration of dilute solution of PVC in Cyclohexanone (0.2% W/V).
The relative viscosity is evaluated by an empirical correlation according to (Xu et al.,
1989) as:
[]
rel 1 3Ln (rel )
4C
(20)
Where intrinsic viscosity is related to weight molecular weight by (Xie et al., 1991b):
5.30 105 Mw0.828
(21)
According to (Xie et al., 1991a) Kinetic parameters of VCM polymerization that are used
in the model contain:
E
Kd1 K0 exp
RT
Kt1 1.3 1012 exp(
(22)
4200
)
RT
K p1 10.4 Kt10.5 exp(
(23)
1902
)
T
(24)
10
These kinetic parameters for diffusion controlled conditions are modeled using thefree
volume theory as follows (Xie et al., 1991b)
1 1
Kd 2 Kd1 exp C
V
Vf
fp
(25)
1
1
Kt 2 Kt1 exp A
V fp V f ,crit
(26)
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1 1
K p 2 K p1 exp B
V fp V f
(27)
1 1
K p 2 f 1/2 ( K p1 f 1/2 ) Xf exp D
V
Vf
fp
(28)
Where,
A 6.64 106 exp(4986 / T )
(29)
B 1.85 103 exp(2595 / T )
(30)
C 4.77 102 exp(2291/ T )
(31)
D 4.01 104 exp(3464 / T )
(32)
The free volume fraction of the polymer-monomer mixture Vf, pure polymer Vfp and pure
monomer Vfm are calculated by (Xie et al., 1991b):
V f V fp 2 V fm (1 2 )
(33)
V fp 0.025 p (T Tgp )
(34)
V fm 0.025 m (T Tgm )
(35)
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The polymer volume fraction ϕ2 at the glassy transition state can be expressed as:
2
m (T Tgm )
m (T Tgm ) p (T Tgp )
(36)
The critical free volumeis given by:
V f ,crit 0.8V fm
(37)
The glassy state transition temperature and the thermal expansion factors (α) for VCM
and PVC as follows:
Chemical Engineering Communications
Tgm 70 ( K )
(38)
Tgp 87.1 0.132T (C)
(39)
m 9.98 104 ( K 1 )
(40)
p 5.47 104 ( K 1 )
(41)
Model Solution
As mentioned, the aim of this work is to determine an initiator dosage trajectory for
reducing batch time by which the conversion and the product specifications (MW and
MWD) which are obtained are identical to those achieved by the conventional
polymerization. The initiator dosage trajectory that provides both the highest reaction rate
and a given conversion must be determined such that for every instant of time during the
batch processing, the heat released does not exceed the maximum heat removal capacity
of the reactor. A 4th order Rung-Kutta algorithm was applied to solve first order ordinary
12
differential equations (ODEs). The step time size was specified 60s to produce a
convergent solution.
Optimization Approach
Given that PVC polymerization process is time-consuming and the experimental
determination of an optimal initiator dose is difficult, estimation of the optimum
continuous dosage trajectory can be conducted more readily using an optimization
algorithm. Such optimization algorithms allow researchers to determine an optimal
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initiator trajectory in which the reaction rate at any time establishes its maximum
permission value more readily than is the case when using a trial and error method.
Particle Swarm Optimization algorithm (PSO) is one of the latest evolutionary
optimization methods developed by Eberhart and Kennedy (Eberhart and Kennedy,
1995). PSO can optimize the solution to a problem by maintaining a population of
candidate solutions (particles) and moving these particles within the search-space (Santos
et al., 2012). PSO initially selects candidate solutions randomly and this is initialized with
a group of random particles (solutions) followed by searching for optima by updating
generations. At any iteration, each particle is updated by following two best values. The
first one is the best fitness (pbest). Another best value that is tracked by the particle
swarm optimizer is the best value obtained so far by any particle in the population. This
best value is a global best and called gbest (Abdel-Magid and Abido, 2004).
13
After determining the two best values, the particle updates its velocity and positions using
its current position and velocity according the following equations (Shi and Eberhart,
1998):
Vi t 1 wVi t C1 rand (0,1)( pbesti X it ) C2 rand (0,1)( gbestt X it )
X it 1 X it Vi t 1
(42)
(43)
where, Vit and Vit+1 are the current and the new velocity of particle i, and Xit and Xit+1 are
the current and the new positions of particle i. The pbest and gbest are defined as stated
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above. The rand is a random number between (0, 1). C1 andC2 are learning factors and
the "w" is inertia weight used to ensure convergence (Panda and Padhy, 2008). It should
be noted that the random parameters terms (rand) in the velocity formula guarantee
reaching the global optimum point(Hassan et al., 2005). As regards Eq. (42), the current
velocity in a PSO consists of three parts: momentum, cognitive, and social. The balance
of these three parts allow for obtaining a high performance PSO algorithm, and this
depends on the values of parameters w, C1and C2(Panda and Padhy, 2008). Although the
values of 1, 2 and 2 were used in the original PSO algorithm for w, C1, and C2,
respectively, Eberhart and Kennedy suggested the ranges of 0.4 to 1.4, 1.5 to 2, and 2 to
2.5 for them (Eberhart and Kennedy, 1995). In general, the values of these parameters
depend upon the problem under consideration. In this study, the appropriate values of
parameters C1, C2 and w are ultimately considered to be 0.9 and 1.8 and 0.5 respectively.
The operational target is achieving the minimum of the overall batch time of
polymerization for a certain limiting conversion and reaction rate, which would increase
14
the productivity. In this case, the initiator concentration during the process is the value
which should be optimized.
The important constraints in the operation are the limitation of maximum reaction rateand
final conversion, both of which are determined by the user.
The maximum capacity of the cooling system of the reactor is dependent on the reaction
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rate and can be calculated from:
dX
Qmax H M 0
dt max
where, ∆H and
dX
dt max
(44)
are the enthalpy of reaction and the possible maximum reaction
rate, respectively.
It is obvious that the reaction rate at any time during polymerization must not exceed the
maximum value, as shown below:
dX
dX
dt at any time dt max
(45)
dX
where, dt at each stage is obtained from Eqs. (5, 11 and 14).
Material
In order to validate the model predictions, suspension polymerization experiments were
carried out in a 48 L stainless steel-jacketed reaction vessel equipped with four tubular
baffles and an agitator consisting of two six-flat-blade turbines. The temperature of the
15
mixture in the reactor was kept constant at the desired value, via flowing cold water in
the jacket. The temperature of the reaction mixture, jacket input/output and reactor
pressure were recorded by data logger. A special sampler device was designed for
extracting samples during the process. Fig. 1 illustrates a schematic diagram of
polymerization reactor. The materials used are listed in Table І.
Diisobutyryl peroxide is a fast initiator synthesized according to US 70,053,161(2006),
using Potassium Hydroxide (KOH), Hydrogen peroxide (H2O2), Isobutyryl Chloride (i-
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BuCl) and n-Hexane (all from Merck Co.). Diisobutyryl peroxide is obtained with a
purity of 29.7 wt% in n-Hexane and active oxygen of 2.73%. The physical and chemical
properties of obtained Diisobutyryl peroxide is equivalent to Trigonox 187-C30 produced
by the Akzo Nobel company.
Polymerization Procedure
Suspension polymerizations of VCM were carried out under two procedures for initiator
addition: a conventional process (in a commercial producing plant), wherein a mild
initiator (Perkadox 26) is entirely charged at once at the beginning of the polymerization
and a new process in which a fast initiator (Diisobutyryl peroxide) is dosed to a reactor
during the course of the polymerization reaction. The reactor was charged with 12200g of
VCM, 18500g DM Water, 235g HPC and 245g HPMC (3.5wt. % solution in water) as
the primary suspending agents and 16.7g Span 20 as a nonionic secondary suspending
agent. The reactor temperature was controlled by adjusting the water flow rate of a
circulator into the jacket. In a conventional experiment, the amount of initiator, Perkadox
16
1
15 1
26 (Dimyristyl peroxydicarbonate, A 2.82 10 s , Eactivation 124.1kJ mol ), was
14.3g, which was added to the reactor before the VCM charging. The mixture of reaction
was heated up to the polymerization temperature of 52 °C in ≈20 min by flowing hot
water in the jacket. In the new process, after reaching the polymerization temperature,
1
14 1
12g Diisobutyryl peroxide ( A 3.37 10 s , Eactivation 109.06 kJ mol ) as a fast
initiator, was dosed to the reaction mixture during the process. In all experiments, the
temperature in the reactor was regulated to a value of 52 °C with an accuracy ± 0.3oC
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until reaching a sharp pressure drop in the reactor and a significant reduction in the
reaction rate of polymerization (critical conversion). The reaction mixture was then
heated to 62 °C to remove unreacted VCM. Sampling was carried out during the
polymerization course using a sampler device.
At the end of the process, the reactor was rapidly cooled to 30°C, followed by the
condensation of the remaining VCM in a storage vessel. Slurry obtained was filtered and
dried at 55° C for 24 hours in an oven preparing PVC grains.
Characterization Of The S-PVC Particles
The final conversion was calculated by gravimetry of the dried PVC grains. The
conversion during the process was obtained using two methods: weighing the extracted
samples, and energy balance around the isolated reactor. The conversion versus time
relationship was obtained by weighing each sample, according to:
X
mp (1 f r )
mt f r
(26)
17
where mP is the mass of dried polymer in the sample, mt is the total mass of sample, fr is
the VCM/water mass ratio initially present in the reactor. Another method of
measurement of the conversion is energy balanced around the isolated reactor, according
to (Nagy and Agachi, 1997):
Vmix mixCpmix
dT
dX
H M0
U (T Tj )
dt
dt
(27)
where, Vmix, ρmix and Cpmix are the volume, density and specific heat of the mixture in the
reactor, Tj is jacket average temperature recorded by the data logger and U is the overall
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heat transfer coefficient at the walls of the reactor which was obtained experimentally.
The K value as a molecular characteristic was calculated using the dilute-solution
viscosity measurements of the PVC samples via a viscometer (LAUDA, Proline, pv15)
according to (ISO D3105-1994). The MWs of the samples were measured using gel
permeation chromatography (GPC Agilent 1100) with PLgel, 10μm, 300×7.5 mm
columns, a Tetrahydrofuran (THF) solution of PVC at 30oC, and a 1 ml/min flow rate.
RESULTS AND DISCUSSION
Model Validation
The model results (conversion, K-value and average molecular weight) were verified by
the experimental data. We sought to evaluate the predictions of the model at various
doses of the initiator in the method of continuous dosing of the initiator as well as at
regular initiator addition. Two mentioned procedures in the polymerization process for
adding the initiator were applied; in the first procedure, according to a conventional
process, total mild initiator, Perkadox 26, was added to the reactor at the beginning of the
18
process. In the second procedure, the dosage of the fast initiator (Diisobutyryl peroxide)
1
was first kept constant at about 0.36 g min for 20 min, and was then decreased to
1
1
0.0686 g min from 21 to 56min, and once again was decreased to 0.04 g min within a
60-minute time period. The implementation of such an optimal initiator dosage strategy
caused the polymerization rate to be kept constant during the time of the polymerization.
It should be noted that the reason for dosing the initiator in three successive steps, instead
of the optimum dosage rate predicted by the model (using particle swarm optimization
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(PSO) algorithm), is facilitation during the dosing operation. In the other words, the used
initiator dosage policy is the average of optimum initiator trajectory during three stages
of time. The initiator dosage was stopped at a critical conversion (Xf). The predicted and
used optimum trajectories of the fast initiator dosage are shown in Fig. 2.
Fig. 3 compares the model predictions and experimental data for conversion during the
process in both experiments: continuous dosage of the fast initiator and non-continuous
of Perkadox 26. The results obtained from the energy balance method are compared to
above data in the Fig. 3. It can be seen that the present model predictions are in good
agreement with the experimental data and energy balance results for both experiments.
In this model, efficiency of Perkadox 26 and Diisobutyryl peroxide were adjusted to be
0.8 and 0.6, respectively. Traveling through a long path in the continuous aqueous phase
and crossing from the VCM droplets/water interface by a fast initiator in process with
continuous dosage system leads to decrease initiator efficiency (Mrázek et al., 1991).
19
Also, adsorption of the fast initiator on the surfaces of formed particles alters the initiator
partition coefficient between the monomer and polymer phases such that most of the
initiator remains in polymer phase. This reason is also corroborated by the known affinity
peroxy initiators for PVC chains (Mrázek et al., 1991). The initiator partition coefficient
(KI) for a continuous dosage system was estimated by fitting the model with conversiontime data (KI=0.9). A value of 0.77 has been determined by Xie, et al. for conventional
system (Xie et al., 1991a).
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Figs. 4 and 5 also show the comparison between the experimental data and model results
for K value and average molecular-weights of both experiments. Once again, there is a
reasonable agreement between the model and the experimental results.
Effect Of Continuous Dosage On PVC Process
The goal of the work is to find an optimal trajectory for initiator dosages in order to
establish a balance between the maximum permissible cooling capacity of the reactor and
minimum batch time. In this regard, the dose level of the initial stage of the fast initiator
dosage as the most important dosage step, and the dose level during the process were
optimized by the particle swarm optimization (PSO) algorithm in which several attempts
were made to find a continuous initiator dosage trajectory by use of simulations so as to
minimize the polymerization time for the final conversion of 80% (the reaction rate does
not exceed the pre-defined value at any time). In the initial stage, the initiator was dosed
in such a way that the reaction rate changed from zero to the desired value. While the
time required for the initial stage of the initiator dosage for all of the pre-defined reaction
20
rates was found to be 20 minutes, the dose level of the initiator increases with increasing
pre-defined reaction rates. In order to clarify this subject, several runs with different
initial stage duration are compared as illustrated in Fig. 6. Once the dosing comprises an
initial stage having a duration that is less than 20 minutes (i.e. 10 min), more amount of
initiator is required to achieve the desired reaction rate (here 0.61%/min as the maximum
permissible reaction rate) which this causes an excess initiator to remain in the process
and to affect the reaction rate over the next steps. This level of the initiator with very low
half-life leads to produce high radical concentration and a sensible acceleration of the
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reaction and causing the reaction rate to exceed from the maximum permissible reaction
rate. On the other side, when the initial stage of initiator dosing is more than 20 minutes
(35 min- Fig.6), the desired reaction rate is delayed and hence the time of polymerization
process is increased. As a result, an initiator dosing trajectory with a 20 minutes initial
stage is considered to balance between the maximum permissible reaction rate and
minimum polymerization process time.
In order to evaluate the influence of continuous dosage of a fast initiator (Diisobutyryl
peroxide) on the suspension polymerization of VCM and the resin properties, several
simulation runs were conducted and then compared to the case in which a mild initiator
(Perkadox 26) was added at the beginning of the polymerization (conventional process).
The results obtained from different runs are presented in Table II.
The evaluation of conversion during the polymerization process and the reaction rate of
the polymerization in respect to conversion for the aforementioned runs are shown in
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Figs. 7 and 8, respectively. The maximum reaction rate and conversion for run 1
(conventional run as a reference run) obtained 0.61 percent/min and 80%, respectively.
It is now tried to find an initiator dosage trajectory minimizing the polymerization time
for the final conversion identical to Run 1 (80%), by simulations. This would be
obviously obtained if the reaction rate was kept constant over the entire course of the
polymerization at a constant value. In order to study the effect of the maximum
permissible reaction rate on resin properties, runs 2-4 were performed at three different
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allowable reaction rates, i.e. lesser, larger and identical to that of conventional process
(0.61 %/min). These Runs show that if we allow to choose the maximum cooling
capacity of the reactor respect to the permissible reaction rate, what affect on
polymerization time and resin properties. Such trajectories are shown in Fig. 9. In all
these trajectories, the initiator dosing comprises a first stage which lasted 20 min during
which the level of dosage remains constant and the reaction rate reaches to permissible
value. Just after that a second stage begins, during which the dosage of the initiator
decreases until the level of dosage reaches zero to keep the reaction rate in constant
amount.
As shown in Fig. 8, by continuous dosage of a fast initiator (in different allowable
reaction rates), the reaction rate remained constant during the course of polymerization
processes. The results illustrate that applying a continuous dosage mode of a fast initiator
leads a 31-65% reduction in the total polymerization time required for a given
conversion, as compared to the case in which only one mild initiator was added at the
22
beginning of the process. The higher permissible maximum reaction rates the more
reaction rate and thus, the further of the reactor cooling capacity is used, resulting in the
lower reaction time.
It can be observed in Figs. 7 and 8 that a twofold increase in the maximum permissible
reaction rate (it can be achieved by increasing the amount of the initiator), reduces total
polymerization time up to 50%.
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Run 5 correspond to a comparative case in which the total amount of the initiator
(identical to that of Run1) is added at the beginning of the polymerization reaction. In this
case, initiator decomposition occurs rapidly and thus, the free radical source is no longer
available to continue polymerization, and it finishes at the middle of the process,
resulting in the lowest final conversion level (see Fig. 8).
Fig. 10 indicates the molecular characteristics of the final product, in terms of the weightaverage molecular weights. As it is known that the molecular weight of PVC is little
affected by type and concentration of the initiator (Kiparissides et al., 1997; Xie et al.,
1991b), molecular specifications decrease slightly with the reaction rate. Continuous fast
initiator dosage started at the beginning of the process increases the production of free
radicals and the subsequent termination rate leading a molecular weight difference with
Run1. This phenomenon is more pronounced during the early stage of conversions where
monomer phase is predominant and polymerization occurs homogenously.
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The evolution of the residual level of initiator for different initiator dosage trajectories are
shown in Fig. 11. This figure shows while in Run1 some amount of initiator residue
finally, initiator residual in a continuous dosing of very fast initiators during
polymerization reactions reach zero. Therefore, residual initiator in processes with
Diisobutyryl peroxide as a fast initiator (Runs 2-5), is much less than in a process with
Perkadox 26 acting as a mild initiator (Run 1). Using a very efficient dosage of a fast
initiator, render a resin after polymerization with very low residual initiator levels.
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CONCLUSION
The adopted model using PSO algorithm was applied to predict an optimal initiator
dosage trajectory in vinyl chloride suspension polymerization, and this validated by
experimental data. The model predictions suggest that applying an initiator dosage
system in a proper trajectory can dramatically improve productivity by reducing the
polymerization time for a certain final conversion compared to regular reactions in which
the total amount of initiator is added at the beginning of the polymerization process. The
experimental and theoretical model results show that the use of an optimal continuous
dosage trajectory during the polymerization (Run 3) decreases total polymerization time
up to 53% for given polymer specifications, in comparison with the conventional case. It
was shown that as initiator doses are increased, the required heat removal rate increases
and the polymerization time reduces to a remarkable degree, and polymer specifications
such as K value and average molecular weight only slightly decrease. The morphology
and molecular characteristics of PVC grains produced under an initiator dosage system is
currently under examination and the results will be presented in forthcoming papers.
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ACKNOWLEDGMENTS
Partial financial support of Petrochemical Research and Technology Company, through
Contract 870429202 is gratefully appreciated.
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Table І. Materials Used in the Suspension Polymerization of Vinyl Chloride.
Name
Role
Trade
Manufacturer
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name
Vinyl Chloride (VC)
Monomer
Arvand Petrochemical Co., Iran
Hydroxypropylmetyl
Primary suspending
Methocel
Shin-Etsu Chemical Co., Tokyo,
cellulose (HPMC)
agent
65SH-50
Japan
Hydroxylpropyl
Primary suspending
Klucle J
Hercules International, Ltd.,
cellulose (HPC)
agent
Sorbitanmonolaurate
Secondary suspending
Huntington, WV
Span 20
agent
Beckmann Chemikalien KG
(Becksurf 7125), Bassum,
Germany
Dimyristyl
Initiator
peroxydicarbonate
Perkadox
Akzo Nobel Co.(Amersfoort,
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The Netherlands)
(MYPC)
Diisobutyryl peroxide
Initiator
Petrochemical Research &
Technology Co.
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Table II. Effect of continuous dosage of fast initiator on S-PVC polymerization and
comparing with non-continuous dosage of initiator.
Initiator type
Dosage
Initia
Convers Poly.
Maximum
ent 1
Run
Perkadox 26
type
Non-
tor
14.3
ion (%)
80
time
320
reaction rate
0.61
Run 2
Diisobutyryl
Continuous
8.25
80
220
0.41
Run 3
Diisobutyryl
Continuous
12
80
150
0.61
Run 4
Diisobutyryl
Continuous
14.65
80
110
0.81
Run 5
Diisobutyryl
Non-
12
30.8
151
0.65
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Experim
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Figure 1. Schematic diagram of polymerization reactor.
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Figure 2. Predicted and used optimum trajectories of the fast initiator dosage
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(Diisobutyryl peroxide).
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Figure 3. Comparison between experimental data (sampling and energy balance) and
model predictions for conversion during process for continuous dosage of Diisobutyryl
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peroxide and non-continuous of Perkadox 26.
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Figure 4. Comparison between experimental data and model predictions for K value vs.
conversion at two runs; for continuous dosage of Diisobutyryl peroxide and non-
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continuous of Perkadox 26.
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Figure 5. Comparison between experimental data and model predictions for molecular
weights during process at (a): continuous dosage of Diisobutyryl peroxide and (b): non-
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continuous of Perkadox 26.
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Figure 6. Reaction rate vs. time for different duration of initial stage in initiator dosing.
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Figure 7. Conversion during process for different simulation runs.
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Figure 8. Reaction rate of polymerization vs. conversion for different simulation runs.
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Figure 9. Initiator dosage trajectory of Diisobutyryl peroxide during simulation runs 2-4.
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Figure 10. weight-average molecular weights of PVC vs. conversion for different
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simulation runs.
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Figure 11. Residual level of initiator for different simulation runs.
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