Design of a Continuous Distillation Column for a Multi Component Mixture
February 9, 2017 | Author: Serkan | Category: N/A
Short Description
Separation of multicomponent mixtures is very hard and expensive method in industry. For high purity products and high p...
Description
REPORT TO DEP EPARTMENT ARTMENT OF CHEMICAL ENGINEERING EGE UNIVERSITY FOR COURSE: CHE386 CONCEPTUAL DESIGN II
DESIGN REPORT IV
DESIGN OF A CONTINUOUS DISTILLATION COLUMN FOR A MULTICOMPONENT MIXTURE
SUBMITTED TO
Y.Doc.Dr. Serap CESUR SUBMISSION D ATE
25/05/2010 GROUP 3
05070008901 05070008103 05070008849 05060008091 05060008017
Ürün ARDA Berna KAYA Demet ACARGİL M. Serkan ACARSER Tayfun EVCİL
MAY 2010 Bornova- İZMİR
SUMMARY
Separation of multicomponent mixtures is very hard and expensive method in industry. For high purity products and high percentage recovery, continuous distillation columns are used. In this study, a saturated vapor mixture which has 5 different components is tried to be separated and with the help of assumptions, simplifications the plate type distillation column design methods is tried to be explored. In this report you can find the information about shortcut design in ideal and real calculations, using the SRK model. The necessary assumptions were done for both real and ideal calculations, and with the help of Fenske, Underwood and Kirkbridge equations, the number of plates were found.
i
TABLE OF TABLE OF CONTENTS CONTENTS
Summary
.......................................... ................................................................ ............................................ ............................................ ................................ .......... i
1.0 Introduction Introduction
.......................................... ................................................................ ............................................ .......................................... .................... 1
................................................................ ............................................ ............................................ ............................... ......... 2.0 Results ..........................................
2.1 Ideal System
............................................ .................................................................. ............................................ ................................... ............. 3
2.2 Real System (Non-Ideal) 3.0 Discussion and Conclusion 4.0 Nomenclature Nomenclature 5.0 References 6.0 Appendix
3
............................................ .................................................................. ...................................... ................ 6 ......................................... ............................................................... ......................................... ................... 14
............................................ .................................................................. ............................................ .................................... .............. 18
......................................... ............................................................... ............................................ ............................................ ...................... 19
........................................... ................................................................. ............................................ ............................................ ...................... 20
6.1 Ideal System
............................................ .................................................................. ............................................ ................................. ........... 20
6.2 Real System (Non-Ideal)
........................................... ................................................................. ..................................... ............... 27
1.0 INTRODUCTION
Distillation is probably the most widely used separation process in the chemical and allied industries; its applications ranging from the rectification of alcohol, which has been practiced since antiquity, to the fractionation of crude oil. A good understanding of methods used for correlating vapour-liquid equilibrium data is essential to the understanding of distillation and other equilibrium-staged processes. Distillation column design The design of a distillation column can be divided into the following steps:
1. Specify the degree of separation required: set product specifications. 2. Select the operating conditions: batch or continuous; operating pressure. 3. Select the type of contacting device: plates or packing. 4. Determine the stage and reflux requirements: the number of equilibrium stages. 5. Size the column: diameter, number of real stages. 6. Design the column internals: plates, distributors, packing supports. 7. Mechanical design: vessel and internal fittings. The principal step will be to determine the stage and reflux requirements. This is a relatively simple procedure when the feed is a binary mixture, but a complex and difficult task when the feed contains contai ns more than two components (multicomponent systems).
Figure 1. Distillation column (a) Basic column (b) Multiple feeds and side streams
-1-
Process Description The separation of liquid mixtures by distillation depends on differences in volatility between the components. The greater the relative volatilities, the easier the separation. The basic equipment required for continuous distillation is shown in Figure1. Vapor flows up the column and liquid counter-currently counter-currently down down the column. The vapor and liquid are brought into contact on plates, or packing. Part of the condensate from the condenser is returned to the top of the column to provide liquid flow above the feed point (reflux), and part of the liquid from the base of the column is vaporized in the reboiler and returned to provide the vapor flow.
In the section below the feed, the more volatile components are stripped from the liquid and this is known as the stripping section. Above the feed, the concentration of the more volatile components is increased and this is called the enrichment, or more commonly, the rectifying section . Figure1a shows a column producing two product streams, referred to as tops and bottoms , from a single feed. Columns are occasionally used with more than one feed, and with side streams withdrawn at points up the column, Figure1b. This does not alter the basic operation, but complicates the analysis of the process, to some extent. If the process requirement is to strip a volatile component from a relatively nonvolatile solvent, the rectifying section may be omitted, and the column would then be called a stripping column. In some operations, where the top product is required as a vapor, only sufficient liquid is condensed to provide the reflux flow to the column, and the condenser is referred to as a partial condenser. When the liquid is totally condensed, the liquid returned to the column will have the same composition as the top product. In a partial condenser the reflux will be in equilibrium with the vapor leaving the condenser. Virtually pure top and bottom products can be obtained in a single column from a binary feed, but where the feed contains more than two components; only a single “pure” product can be produced, either from the top or bottom of the column. Several columns will be needed to separate a multicomponent feed into its constituent parts. The problem of determining the stage and reflux requirements for multicomponent distillations is much more complex than for binary mixtures. With a multicomponent mixture, fixing one component composition does not uniquely determine the other component compositions and the stage temperature. Also when the feed contains more than two components it is not possible to specify the complete composition of the top and bottom products independently. The separation between the top and bottom products is specified by setting limits on two “key” components, between which it is desired to make the separation.
SHORT-CUT METHODS FOR STAGE AND REFLUX REQUIREMENTS Most of the short-cut methods were developed for the design of separation columns for hydrocarbon systems in the petroleum and petrochemical systems industries, and caution must be exercised when applying them to other systems. They usually depend on the assumption of constant relative volatility, and should not be used for severely non-ideal systems. In this project, during the shortcut calculations, Fenske, Underwood, Gilliand and Kirkbridge Equations were used. Trial and error procedures were all made in excel.
-2-
2.0 RESULTS 2.1 Ideal System Table 1 . Properties of
No
Name
Components Antoine Constants A B
M w,i ρ i w,i 3 [kg/kmol] [kg/m ]
Z i i 1 λ i [%] C [kJ/mol]
1
Methanol
32.04
791.8
7.87863
1473.11
230
15
35.14
2
Ethanol
46.07
789
8.1122
1592.864
226.184
25
38.58
88.15
812
7.27679
1279.01
177.849
25
41.35
74.122
809.8
7.36366
1305.198
173.427
15
43.24
88.15
814.4
7.18246
1287.625
161.33
20
44.83
Neopentanol [Light Key] n-Butanol [Heavy Key]
3 4
1-Pentanol
5
Table 2 .
Calculated Values for the Feed Stream in Ideal System o
100
F [kmol/h]
T dew dew [ C]
113.66
y 1
0.15
n1
15
K 1
5.14
y 2
0.25
n2
25
K 2
3.50
y 3
0.25
n3
25
K 3
1.02
y 4
0.15
n 4
15
K 4 4 [ref.]
0.86
y 5
0.2
n5
20
K 5
0.42
Table 3 .
Calculated Values for the Top Product in Ideal System o
63.6
D [kmol/h]
T dew dew [ C]
96.84
P.R 1
0.98
n1
14.7
y1
0.231
K 1
3.10
P.R 2
0.96
n2
24
y2
0.377
K 2
2.00
P.R 3
0.95
n3
23.75
y3
0.373
K 3
0.55
P.R 4
0.05
n 4
0.75
y 4
0.012
K 4 4 [ref.]
0.45
P.R 5
0.02
n5
0.4
y5
0.006
K 5
0.21
-3-
Table 4 .
Calculated Values for the Bottom Product in Ideal System o
36.4
W [kmol/h]
122.39
T bubble bubble [ C]
P.R 1
0.02
n1
0.3
x 1
0.008
K 1
6.57
y1
P.R 2
0.04
n2
1
x 2
0.027
K 2
4.59
y2
P.R 3
0.05
n3
1.25
x 3
0.034
K 3
1.37
y3
P.R 4
0.95
n 4
14.25
x 4
0.391
P.R 5
0.98
n5
19.6
x 5
0.538
Table 5 .
1.18
K 4 4
0.126
0.047
y
4
0.312
y5
Calculated Values of Vapor Pressures of Components in Ideal System
sat
P i
[mmHg] Feed
Top
sat Methanol [mmHg]
3909.69
2352.49
4991.92
sat Ethanol [mmHg]
2661.98
1517.50
3487.52
sat Neopentanol [mmHg]
774.99
417.46
1039.42
sat n-Butanol [mmHg]
656.70
342.30
894.23
sat 1-Pentanol [mmHg]
316.28
156.67
440.62
P
P P
P P
Table 6 .
0.054
0.461
[ref.]
0.58
K 5
y i =K x i i i i
Bottom
Calculated Values of Relative Volatilities of Components in Ideal System Relative Volatility ,α ri
No
Name
1 2 3 4 5
Feed Stream
Top Product
Bottom Product
Average
Methanol
5.95
6.87
5.58
6.11
Ethanol
4.05
4.43
3.90
4.12
1.18
1.22
1.16
1.19
1.00
1.00
1.00
1.00
0.48
0.46
0.49
0.48
Neopentanol [Light Key] n-Butanol [Heavy Key] 1-Pentanol
Table 7 .
Calculation of Minimum Number of Plates, θ , Minimum Reflux Ratio and Feed Location in Ideal System
N min
34.33
q
0
λ ave,bottom [kJ/mol]
43.836
θ R D,min
-4-
1.075
N R /N S
1.25
3.577
λ ave, top [kJ/mol]
38.914
Calculation of Actual Reflux Ratio, Actual Number of Plates, Feed Location, Height of Column, Condenser Load (Q c ) and Reboiler Load (Q r ) in Ideal System
Table 8.
R D /R D,min
1.5
1.8
2.4
R D,act
5.366
6.439
8.585
X
0.281
0.385
0.522
Y
0.376
0.313
0.238
N act
56
51
46
N S
25
23
20
N R
31
28
26
L [kmol/h]
341.25
409.50
546.00
G [kmol/h]
404.85
473.10
609.60
Q c [kW]
4376.1
5113.9
6589.3
L [kmol/ [kmol/h] h]
341.25
409.50
546.00
[kmol/h]
304.85
373.10
509.60
Q r [kW]
3712.1
4543.1
6205.2
H c [m]
28.5
26.0
23.5
G
Table 9 .
Required Calculations for the Fluid Velocity and Diameter of Column in Ideal System
MW avg [kg/kmol] dot
W [kg/s]
73.34 0.742
3
2.261
ρ liq [kg/m ]
3
811.63
It [m]
0.5
u v [m/s]
0.856
D c [m]
0.698
ρ vap [kg/m ]
-5-
2.2 Real System (Non-Ideal) Table 10. Properties
No
of Components
Name
c [K]
P c [bar] T
ω
ψ
ε
1
Methanol
512.58
80.96
0.566
0.42748
0
2
Ethanol
516.25
63.84
0.637
Z c
σ
3
Neopentanol [Light Key]
550.00
38.80
0.604
0.333333
1
4
n-Butanol [Heavy Key]
562.93
44.13
0.595
Ω
5
1-Pentanol
586.15
38.80
0.594
0.08664
Table 11.
100
T dew dew [ C]
o
106.6
y 1
0.15
n1
15
T r,1
0.741
y 2
0.25
n2
25
T r,2
0.736
y 3
0.25
n3
25
T r,3
0.690
y 4
0.15
n 4
15
T r,4
0.675
y 5
0.2
n5
20
T r,5
0.648
Calculated Values of α SRK,i , a i and b i for the Feed Stream in Non-Ideal System 7
α SRK,1
1.400
a1
1.34*10
α SRK,2
1.442
a2
1.78*10
α SRK,3
1.515
a3
3.49*10
α SRK,4
1.542
a 4
3.27*10
α SRK,5
1.598
a5
4.18*10
Table 13.
[cm3bar/molK]
Calculated Values of y , i n i and T r, r, i for the Feed Stream in Non-Ideal System
F [kmol/h]
Table 12.
R
7
7
7
7
b1
45.61
b2
58.25
b3
102.11
b 4
91.89
b5
108.82
Calculated Values of β β i , q i and Z v i for the Feed Stream in Non-Ideal System
β 1
0.00146
q1
9.321
Z 1
v
0.9870
β 2
0.00187
q2
9.672
Z 2
v
0.9826
β 3
0.00328
q3
10.829
Z 3
v
0.9649
β 4
0.00295
q 4
11.281
Z 4
v
0.9670
β 5
0.00349
q5
12.166
Z 5
v
0.9572
-6-
83.14
Table 14.
I
v
I
v
I
v
I
v
I
v
Calculated Values of I v i , Φv i and Z l i for the Feed Stream in Non-Ideal System v
1
0.00148
Φ
2
0.00190
Φ
3
0.00339
Φ
4
0.00304
Φ
5
0.00364
Φ
Table 15.
v v v v
0.00395
Z 4
l
0.00345
l
0.00370
Z 2
3
0.968
Z 3
4
0.970
5
0.961
Z 5
Calculated Values of I l i , Φl i and K i for the Feed Stream in Non-Ideal System
0.625
Φ2
l
0.604
Φ3
I 4
l
0.618
Φ 4
l
0.665
Φ5
Table 16.
l
0.984
l
I 5
0.00215
2
Φ1
I 3
l
Z 1
0.660
I 2
0.00157
0.988
l
I 1
l
1
l
7.605
K 1
7.70
l
3.078
K 2
3.13
l
0.791
K 3
0.82
l
0.693
K 4
0.71
l
0.545
K 5
0.57
Calculated Values of α of α r,i , x i and f v i for the Feed Stream in Non-Ideal System v
α r,1
10.78
x 1
0.019
f
α r,2
4.38
x 2
0.080
f
α r,3
1.14
x 3
0.306
f
α r,4
1.00
x 4
0.210
f
α r,5
0.79
x 5
0.352
f
Table 17.
l
0.1501
P 1 [bar]
l
0.2491
P 2 [bar]
l
0.2451
P 3 [bar]
l
0.1474
P 4 [bar]
l
0.1947
P 5 [bar]
f 2 f 3 f 4 f 5
v v v
0.1501
2
0.2491
3
0.2451
4
0.1474
5
0.1947
sat
Calculated Values of f i , P i , γ i and for the Feed Stream in Non-Ideal System
l
f 1
v
1
sat
4.237
γ1
1.818
sat
2.822
γ2
1.105
sat
0.804
γ3
0.997
sat
0.672
γ 4
1.044
sat
0.317
γ5
1.741
-7-
Table 18.
Calculated Values of y , i n i and T r, r, i for the Top Product in Non-Ideal System o
63.6
D [kmol/h]
96.98
T dew dew [ C]
P.R 1
0.98
n1
14.7
y1
0.231
T r,1
0.722
P.R 2
0.96
n2
24
y2
0.377
T r,2
0.717
P.R 3
0.95
n3
23.75
y3
0.373
T r,3
0.673
P.R 4
0.05
n 4
0.75
y 4
0.012
T r,4
0.658
P.R 5
0.02
n5
0.4
y5
0.006
T r,5
0.631
Table 19.
Calculated Values of α SRK,i , a i and b i for the Top Product in Non-Ideal System 7
α SRK,1
1.434
a1
1.38*10
α SRK,2
1.479
a2
1.82*10
α SRK,3
1.551
a3
3.57*10
α SRK,4
1.578
a 4
3.35*10
α SRK,5
1.633
a5
4.27*10
Table 20.
7
7
7
7
b1
45.61
b2
58.25
b3
102.11
b 4
91.89
b5
108.82
v
Calculated Values of β i , q i and Z i for the Top Product in Non-Ideal System
β 1
0.00150
q1
9.798
Z 1
v
0.9880
β 2
0.00192
q2
10.181
Z 2
v
0.9828
β 3
0.00336
q3
11.373
Z 3
v
0.9659
β 4
0.00302
q 4
11.840
Z 4
v
0.9673
β 5
0.00358
q5
12.758
Z 5
v
0.9575
Table 21.
I
v
I
v
I
v
I
v
I
v
v
v
l
Calculated Values of I i , Φ i and Z i for the Top Product in Non-Ideal System v
1
0.00152
Φ
2
0.00195
Φ
3
0.00347
Φ
4
0.00312
Φ
5
0.00373
Φ
v v v v
l
0.00187
l
0.00255
l
0.00426
Z 4
l
0.00385
l
0.00430
1
0.987
Z 1
2
0.982
Z 2
3
0.965
Z 3
4
0.967
5
0.958
Z 5
-8-
Table 22.
Calculated Values of I l i , Φl i and K i for the Top Product in Non-Ideal System
l
0.590
Φ1
l
0.560
Φ2
l
0.582
Φ3
l
0.580
Φ 4
l
0.606
Φ5
I 1 I 2 I 3 I 4 I 5
Table 23.
l
3.108
K 1
3.15
l
1.935
K 2
1.97
l
0.551
K 3
0.57
l
0.467
K 4
0.48
l
0.226
K 5
0.24
Calculated Values of α of α r,i , x i and f v i for the Top Product in Non-Ideal System v
α r,1
6.52
x 1
0.073
f
α r,2
4.08
x 2
0.192
f
α r,3
1.18
x 3
0.655
f
α r,4
1.00
x 4
0.024
f
α r,5
0.49
x 5
0.027
f
Table 24.
0.2310
P 1 [bar]
l
0.3755
P 2 [bar]
l
0.3651
P 3 [bar]
l
0.0116
P 4 [bar]
l
0.0061
P 5 [bar]
f 2 f 3 f 4 f 5
Table 25.
v v v
0.2310
2
0.3755
3
0.3651
4
0.0116
5
0.0061
Calculated Values of f l i , P sat i , γ i and for the Top Product in Non-Ideal System
l
f 1
v
1
sat
3.149
γ1
1.000
sat
2.032
γ2
0.964
sat
0.559
γ3
0.997
sat
0.459
γ 4
1.031
sat
0.210
γ5
1.089
Calculated Values of x , i , n i and T r,r, i for the Bottom Product in Non-Ideal System o
36.4
W [kmol/h]
128.5
T bubble bubble [ C]
P.R 1
0.02
n1
0.3
x 1
0.008
T r,1
0.784
P.R 2
0.04
n2
1
x 2
0.027
T r,2
0.778
P.R 3
0.05
n3
1.25
x 3
0.034
T r,3
0.730
P.R 4
0.95
n 4
14.25
x 4
0.391
T r,4
0.713
P.R 5
0.98
n5
19.6
x 5
0.538
T r,5
0.685
-9-
Table 26.
Calculated Values of α SRK,i , a i and b i for the Bottom Product in Non-Ideal System 7
α SRK,1
1.325
a1
1.27*10
α SRK,2
1.361
a2
1.68*10
α SRK,3
1.437
a3
3.31*10
α SRK,4
1.465
a 4
3.11*10
α SRK,5
1.520
a5
3.98*10
Table 27.
7
7
7
7
b1
45.61
b2
58.25
b3
102.11
b 4
91.89
b5
108.82
Calculated Values of β i , q i and Z v i for the Bottom Product in Non-Ideal System
β 1
0.00138
q1
8.341
Z 1
v
0.9892
β 2
0.00177
q2
8.629
Z 2
v
0.9853
β 3
0.00310
q3
9.709
Z 3
v
0.9704
β 4
0.00279
q 4
10.130
Z 4
v
0.9721
β 5
0.00330
q5
10.946
Z 5
v
0.9638
Table 28.
I
v
I
v
I
v
I
v
I
v
Calculated Values of I v i , Φv i and Z l i for the Bottom Product in Non-Ideal System v
1
0.00140
Φ
2
0.00179
Φ
3
0.00319
Φ
4
0.00286
Φ
5
0.00342
Φ
Table 29.
v v v v
0.599
Φ1
l
0.543
Φ2
l
0.548
Φ3
l
0.567
Φ 4
l
0.580
Φ5
I 2 I 3 I 4 I 5
0.00169
l
0.00245
l
0.00425
Z 4
l
0.00365
l
0.00420
0.990
Z 1
2
0.987
Z 2
3
0.973
Z 3
4
0.975
5
0.967
Z 5
Calculated Values of I l i , Φl i and K i for the Bottom Product in Non-Ideal System
l
I 1
l
1
l
8.223
K 1
8.31
l
4.982
K 2
5.05
l
1.576
K 3
1.62
l
1.365
K 4
1.40
l
0.719
K 5
0.74
- 10 -
Table 30.
Calculated Values of α of α r,i , y i and f v i for the Bottom Product in Non-Ideal System v
α r,1
5.93
y1
0.068
f
α r,2
3.60
y2
0.139
f
α r,3
1.16
y3
0.056
f
α r,4
1.00
y 4
0.548
f
α r,5
0.53
y5
0.400
f
Table 31.
v v v v
1
0.0687
2
0.1386
3
0.0548
4
0.5415
5
0.3921
Calculated Values of f l i , P sat i , γ i and for the Bottom Product in Non-Ideal System
l
0.0687
P 1 [bar]
l
0.1386
P 2 [bar]
l
0.0548
P 3 [bar]
l
0.5415
P 4 [bar]
l
0.3921
P 5 [bar]
f 1 f 2 f 3 f 4 f 5
sat
7.840
γ1
0.015
sat
5.572
γ2
0.036
sat
1.685
γ3
0.361
sat
1.464
γ 4
0.481
sat
0.732
γ5
1.801
Table 32.
Calculated Values of Relative Volatilities of Components in Non-Ideal System
No
Name
1 2
Relative Volatility ,α ri
3 4 5
Feed Stream
Top Product
Bottom Product
Average
Methanol
10.78
6.52
5.93
7.47
Ethanol
4.38
4.08
3.60
4.01
1.14
1.18
1.16
1.16
1.00
1.00
1.00
1.00
0.79
0.49
0.53
0.59
Neopentanol [Light Key] n-Butanol [Heavy Key] 1-Pentanol
Table 33.
Calculation of Minimum Number of Plates, θ, Minimum Reflux Ratio and Feed Location in Non-Ideal System
N min
39.56
q
0
λ ave, bottom [kJ/mol]
43.836
θ R D,min
- 11 -
1.051
N R /N S
1.25
3.516
λ ave, top [kJ/mol]
38.914
Table 34.
Calculation of Actual Reflux Ratio, Actual Number of Plates, Feed Location, Height of Column, Condenser Load (Q c ) and Reboiler Load (Q r ) in Ideal System
R D /R D,min
1.5
1.8
2.4
R D,act
5.274
6.328
8.438
X
0.280
0.384
0.522
Y
0.376
0.313
0.238
N act
64
59
53
N S
28
26
24
N R
36
33
29
L [kmol/h]
335.40
402.48
536.64
G [kmol/h]
399.00
466.08
600.24
Q c [kW]
4312.9
5038.0
6488.2
L [kmol/ [kmol/h] h]
335.40
402.48
536.64
[kmol/h]
299.00
366.08
500.24
Q r [kW]
3640.9
4457.7
6091.3
H c [m]
32.5
30.0
27.0
G
Table 35.
Required Calculations for the Fluid Velocity and Diameter of Column in Non-Ideal System
MW avg [kg/kmol] dot
W [kg/s]
89.42 0.904
3
2.715
ρ liq [kg/m ]
3
811.63
It [m]
0.5
u v [m/s]
0.781
D c [m]
0.737
ρ vap [kg/m ]
- 12 -
Table 36. 36.
Calculated Values by Using ChemCAD 6.0.2 for Ideal and Non-Ideal System Ideal System with Raoult’s Law
Non-Ideal System with SRK Method
R D /R D,min
1.5
1.8
2.4
1.5
1.8
2.4
R D,act
5.2821
6.3386
8.4514
62.0107
6.7886
9.0515
N S
29.2254
26.1033
23.2336
31.2342
27.9023
24.8464
N act
57.9572
51.6570
45.8660
5.6572
55.2872
49.1205
Q c [kJ/h]
-1.4678*10
Q r [kJ/h]
1.0981*10
7
7
-1.9449*10
7
7
-2.5049*10
7
7
7
-1.7721*10
-2.0733*10
7
7
7
-2.6756*10
1.5182*10
2.0782*10
1.3445*10
1.6457*10
2.2480*10
R D,min
3.5214
3.5214
3.5214
3.7715
3.7715
3.7715
N min
35.0220
35.0220
35.0220
37.6120
37.6120
37.6120
- 13 -
7
7
3.0 DISCUSSION AND CONCLUSION
The object of this report is to design a multi-component distillation column for ideal and non-ideal situations. Consider the case of the distillation of a multi-component mixture in a multi-stage distillation column. As before, the number number of degrees of freedom is determined by the description rule (i.e., D.O.F. = number of variables set during construction or controlled during operation by by independent means). Generally, all the variables associated with the feed, such as its composition, flow rate and enthalpy are set, as is the column pressure, which leaves four degrees of freedom and two basic types of problems (design and simulation), as was the case for a binary distillation. For a design problem, the goal is to determine the number of plates needed and the location of the feed plate, and the following is generally specified •
•
Separation variable #1, the recovery of the light key component in the top (distillate) product. Separation variable #2, the recovery of the heavy key component in the bottom product.
•
Condenser and reboiler loads
•
Diameter and height of the column
•
The fact that the optimal feed plate is used that minimizes the total number of plates.
•
The reflux ratio.
Generally, in a multi-component distillation column, only two components will exist in significant quantities in both both the bottom and top products. These are the two key components. The heavy non-key components components will essentially all end up in the bottom product while the light non-key components will will essentially all end up in the top product. This is why the separation variables described above are given in terms of the key components. In our process, the components were methanol, ethanol, neopentanol, n-butanol and 1 pentanol. Our feed rate was 100 kmol/h; the light-key component was neopentanol and the heavy-key component was n-butanol. Our mole fractions in the feed were 15%, 25%, 25%,15% and 20% respectively (See Table 2). The separation targets for top and bottom products were 95%. In order to find temperature and equilibrium constants constants for the feed, a sat temperature was assumed. The P values were calculated at this temperature, by using Antoine equation (See Table 5). The equilibrium constants were calculated with this assumed tem temperatu raturre (S (See Table 2) 2). By By us using Go Goal-s al-seeek, ek, we we eq equaliz alizeed
. Th The de dew-point int
temperature was calculated as 113.66°C. According to the calculated temperature, the equilibrium constants were found as 5.14, 3.5, 1.02, 0.86, and 0.42. To calculate relative volatilities of the components, the ratio of K value of each component to the K value of the heavy-key product was taken. After this, the relative volatilities were found as, 5.95, 4.05, 1.18, 1 and 0.48 (See Table 6). - 14 -
In the ideal calculation, since we only had specific target separation for the light-key and heavy- key products were known (which was 95% for light-key at top and 95% for heavy at the bottom), the other separations were assumed 98% for methanol, 96% for ethanol, 95% for neopentanol, 5% for n-butanol and 2% 1-pentanol (See Table 3). The flow rate of top product was found as 63.6 kmol/h. As a result, the mole fractions for the top product were calculated as 0.231, 0.377, 0.373, 0.012, and 0.006 (See Table 3). In order to find temperature and equilibrium constants, a temperature was assumed. The P sat values were calculated at this temperature, by using Antoine equation (See Table 5).The equilibrium constants were calc calcu ulate lated d wit with h thi thiss as assumed umed tem tempera peratu ture re.. By By usi using ng Goaloal-se seek ek,, we we equ equal aliz ized ed
. Th The
dew-point temperature was calculated as 96.84°C.According to the calculated temperature, the equilibrium constants were found as 3.10, 2, 0.55, 0.45, and 0.21 (See Table 3). To calculate relative volatilities of the components, the ratio of K value of each component to the K value of the heavy-key product was taken. After this, the relative volatilities were found as, 6.87, 4.43, 1.22, 1 and 0.46 (See Table 6). In the bottom product, the separations were assumed 2% for methanol, 4% for ethanol, 5% for neopentanol, 95% for n-butanol and 98% 1-pentanol (See Table 4). The flow rate of bottom product was found as 36.4 kmol/h. As a result, the mole fractions for the top product were calculated as 0.008, 0.027, 0.034, 0.391 and 0.538 (See Table 4). In order to find temperature and equilibrium constants, a temperature was assumed. The P sat values were calculated at this temperature, by using Antoine equation (See Table 5). The equilibrium constants were calculated with this assumed temperature. By using Goal-seek, we equalized . The dew-point temperature was calculated as 122.39°C. According to the calculated temperature, the equilibrium constants were found as 6.57, 4.59, 1.37, 1.18 and 0.58 (See Table 4). To calculate relative volatilities of the components, the ratio of K value of each component to the K value of the heavy-key product was taken. After this, the relative volatilities were found as, 5.58, 3.90, 1.16, 1 and 0.49 (See Table 6). The average relative volatilities of the components were determined by taking the geometric mean of the components’ volatilities at the feed, top product and bottom product. The values were 6.11, 4.12, 1.19, 1 and 0.48, respectively (See Table 6). Fenske equation was used to calculate the minimum number of trays. As a result, the minimum plate number was found as 34.33 (See Table 7). To find the minimum reflux ratio, the θ parameter was calculated at saturated vapor condition (q=0), and it must be between the relative volatilities of the light-key and heavy-key component, and was calculated using Goal-seek. As a result, the θ value was found as 1.075. Using Underwood equation, the minimum reflux ratio was determined as 3.57 (See Table 7). The ratio of
was assumed as 1.5, 1.8 and 2.4 respectively and the actual reflux
values were calculated and tabulated (See Table 8).
- 15 -
The Gilliland correlation was used to calculate actual plate number. For this, X and Y parameters were calculated and Nactual was found as 56, 51 and 46, using the Y function and N min value (See Table 8). To determine the feed location, we used Kirkbridge equation. For N actual being 56, the entry location was found as the 26 th tray. The N R and N S values were tabulated (See Table 8). To calculate reboiler and condenser duty, the average latent heat of vaporization was calculated. Our reboiler and condenser were selected as total reboiler and condenser. As a result, the reboiler duty was found as 3712.1kW for R min/R at 1.5. The condenser duty was found as 4376.1kW for the same ratio. Other values were tabulated (See Table 8). The height and diameter of the column were calculated lastly. The diameter was found as 0.698m and the height was 28.5 m. Other values were tabulated (See Table 8 and 9). In the case of the non-ideal system, the critical temperature, critical pressure, density, molecular weight and acentric factor were looked looked up from Ref.4 (See Table 10). The constants for the SRK Model were taken, a temperature was assumed and the reduced temperatures were calculated accordingly. The parameters α SRK , a i, b i , β i and q i were determined. Zv i was calculated using Goal-seek and I v i and Φv i were determined by using the related equations in Ref.2.Same procedure was followed for Z L i , IL i and ΦL i . The equilibrium constants were determined using
. The liquid mole fractions were calculated to be used in
Modified Raoult’s Law. The P i sat values were determined by Antoine equation. The vaporliquid equilibrium was proven by the equality of fugacity coefficients of vapor and liquid phases. The activity coefficient was calculated from Modified Raoult’s Law. The assumed dew- point temperature was checked using the γi and Psat values, and from Goal-seek, the actual dew-point temperatures was calculated as 106.6°C for feed, 96.98°C for top product. Same procedure was applied to the bottom product to find bubble-point temperature, which was found as 128.5°C. The average relative volatilities were calculated and found as 7.47, 4.01, 1.16, 1 and 0.59 respectively (See Table 32). The Fenske, Underwood, Gilliland and Kirkbridge equations were used like in the ideal system calculations. From these equations, N min was found as 39.56, θ was found as 1.051, R min was 3.516. For R min/R as 1.5, 1.8 and 2.4, our reflux ratios were found as 5.274, 6.328 and 8.438 respectively. For R min/R as 1.5, 1.8 and 2.4, N act were found as 64, 59, 53. The feed locations were found and tabulated (See Table 34). The condenser and reboiler duties were calculated like in the ideal system. Q c and Q r were calculated and tabulated (See Table 34). Finally, the diameter and height were calculated and were found as 0.737m and 32.5 m respectively. Other values were tabulated (See Table 34 and 35).
- 16 -
According to these results, it can be seen that the ideal system and non-ideal system are slightly different from each other. For both systems, actual plate numbers decrease with increasing R min min /R. Also, height of the column decreases with increasing R min /R. Both Q c and Q r increase with increasing R min min/R, as expected. In real systems, the relative volatilities of components are greater than the relative volatilities of ideal system. Also, the number of plates used are greater than that of ideal systems. The condenser and reboiler duties of real systems are less than the ideal system’s duties. The diameter and height of the column in real systems are greater than the diameter and height of the column in ideal systems. Finally, the most suitable reflux ratio for the real system can be selected within the calculation of total and operation costs. However, the optimum reflux ratio can be chosen without any calculations of costs and it can be seen in Table 34 as 1.8 for this project. In conclusion, the calculated values by using ChemCAD for the ideal and non ideal systems were tabulated in table 36.
- 17 -
4.0 NOMENCLATURE
Symbol
Name
Unit
M w,i
Molecular Weight of i Component
[kg/kmol]
ρi
Density of i Component
[kg/m3]
ρ vap
Vapor Density of i Component
[kg/m3]
ρ liquid
Liquid Density of i Component
[kg/m3]
F
Mol Number of Feed Stream
[kmol/h]
D
Mol Number of Top Product
[kmol/h]
W
Mol Number of Bottom Product
[kmol/h]
ni
Mole Number of i Component
[kmol/h]
xi
Mole Fraction of i Component
P.R. i
Percentage Recovery of i Component
Ki
Distribution Coefficient of of i Component
Psat
Saturated Vapor Pressure
[bar]
Pt
Total Pressure
[bar]
αi
Relative Volatilities of i Component
N min
Minimum Number of Plate
N act
Actual Number of Plate
NS
Number of Plate of Stripping Section
N R
Number of Plate of Enriching Section
R D,min
Minimum Reflux Ratio
R D,act
Actual Reflux Ratio
λ i
Latent Heat of Vaporization
MW
Molecular Weight of Mixing
uv
Fluid Velocity
[m/s]
Dc
Diameter of Distillation Column
[m]
T r
Reduce Temperature
f
Fugacity
Φ
Fugacity Coefficient
T
Temperature
[oC]
Tc
Critical Temperature
[K]
Pc
Critical Pressure
[bar]
Q r
Reboiler Load
[kJ/s]
Qc
Condenser Load
[kJ/s]
- 18 -
5.0 REFERENCES
1.
Coulson, J.M., Richardson, J.F., Chemical Engineering Series - Chemical Brit ain Pergamon Press, 1977. Engineering Design, Vol. 6, 4th Ed., Great Britain
2.
J.M. Smith, H.C. Van Ness, M.M. Abbott, Abbott, Introduction to Chemical Engineering th Thermodynamics , 2005, 7 Ed., Mc Graw Hill Company, Singapore.
3.
Felder, R.M., Rousseau, R.W., Elementary Principles of Chemical Process , 2nd Ed., John Willey and Sons Inc, USA, 1986.
4.
Yaws C.L., Yaws' Handbook of Thermodynamic and Physical Properties of Chemical Compounds, Lamar University, Beaumont, Texas, Norwich, New York, 2004
- 19 -
6.0 APPENDIX 6.1 Ideal System G (See Table 4). L F=100 kmol/h kmol/h n1=15 kmol/h n2=25 kmol/h n3=25 kmol/h n4=15 kmol/h n5=20 kmol/h
G
L W
D
D=63.6 kmol/h n1=14.7 kmol/h n2=24 kmol/h n3=23.75 kmol/h n4=0.75 kmol/h n5=0.4 kmol/h
W=36.4 kmol/h n1=0.3 kmol/h n2=1 kmol/h n3=1.25 kmol/h n4=14.25 kmol/h n5=19.6 kmol/h
The mixture of methanol, ethanol, neopentanol, n-butanol and 1-pentanol was fed to the column as 100 kmol/h. The given data for the feed, top and bottom product was tabulated in Table 2, 3, 4.
Calculation of Mole Numbers of Components in Feed Stream
F= 100
kmol h
x1 = 0.15
n1 = 0.15 ×100 = 15 kmol h
x2 = 0.25
n2 = 0.25 ×100 = 25 kmol h
x3 = 0.25
n3 = 0.25 ×100 = 25 kmol h
x4 = 0.15
n4 = 0.15 ×100 = 15 kmol h
x5 = 0.20
n5 = 0.20 ×100 = 20 kmol h
Assumption of Percentage Recoveries for Top Product
P.R .1 = 0.98 P.R .2 = 0.96 P.R .3 = 0.95 P.R .4 = 0.05 P.R .5 = 0.02
× P.Ri ni = n Fi Fi n1 =15 × 0.98 = 14 14.7 kmol / h n2 = 25 × 0.96 = 24 2 4 kmol / h n3 = 25 × 0.95 = 23 23.75 kmol / h n4 = 15 × 0.05 = 0.75 kmol / h n5 = 20 × 0.02 = 0.4 kmol / h
- 20 -
x1 =14.7 / 63.6 = 0.231
xdi = ni / D
x2 = 24 / 63.6 = 0.377
D = 14.7 + 24 + 23.75 + 0.75 + 0.4
x3 = 23.75 / 63.6 = 0.373
D= 63.6 kmo/l h
x4 = 0.75 / 63.6 = 0.012 x5 = 0.4 / 63.6 = 0.006
Assumption of Percentage Recoveries for the Bottom Product
ni = n Fi Fi × P.Ri
P.R.1 =1 − 0.98 = 0.02
n1 = 15 × 0.02 = 0. 0 .3kmol / h
P.R.2 = 1 − 0.96 = 0.04
n2 = 25 × 0.04 = 1kmol / h
P.R.3 =1 − 0.95 = 0.05
n3 = 25 × 0.05 =1.25 kmol / h
P.R.4 = 1 − 0.05 = 0.95
n4 = 15 × 0.95 = 14 14.25 kmol / h
P.R.5 = 1 − 0.02 = 0.98
n5 = 20 × 0.98 = 19 19.6 kmol / h x1 = 0.3/ 36.4 36.4 = 0.00 0.008 8
xdi = ni / W
x2 = 1/ 36.4 = 0.027
W = 0.3 + 1 + 1.25 + 14.25 +19.6
x3 =1.25 1.25 / 36.4 36.4 = 0.03 0.034 4
W = 36.4kmol / h
x4 = 14.2 14.25 5 / 36.4 36.4 = 0.3 0.391 x5 = 19.6 19.6 / 36.4 36.4 = 0.53 .538
Calculation of Temperature, K-values & Relative Volatilities for the Feed Stream
Dew point temperature for feed Dew point temperature for the feed was assumed as 100 oC. All calculations was done c
∑
by using this temperature in excel. However xi = i =1
c
yi
∑ K i =1
= 1.00
value could not be
i
obtained. So the dew point temperature was calculated as 113.66 oC by using “Goal Seek” method in Excel and shown below. Ki = yi / xi yi
∑ x = ∑ K = 1.00 i
i
i
i
B log P = A−sat T in C; P oin mmHg ( A, B an a nd C c on onstants we w ere sh s hown in in Ta Table 2) T + C Tdew = 113.66 o C t
( feed stream)
= P 760 mmHg
log
methanol
at 7.87863s− =P
1473.11 113. 113.66 66 + 230 230
;
=P3909.69sat
methanol
For other components see in Table 5.
- 21 -
mmHg
K i =
sat
Pi
K ethanol =
sat P ethanol
=
Pt
K n-butanol = αi =
K methanol =
,
Pt
2661.98 760
sat P n-butanol
P t
K i
,
K
=
P methanol P t
656.70
K n-butanol
α n-butanol ,n-butanol =
K n-butanol K n-butanol
3.5 0.86
=
K 1-pentanol =
K methanol
=
K
= 4.05 ,
0.86 0.86
=1
= 5.14
K neopentanol =
,
α methanol,n-butanol =
=
760
= 0.86 ,
760
K ethanol
=
3909.69
= 3.5
HK
α ethanol ,n-butanol =
sat
sat P neopentanol
P t
P 1 s−at pentanol P t
=
774.99 760
316.28 760
= 1.02
= 0.42
5.14
= 5.95 0.86 n -butanol α neopentanol,n-butanol = α 1- pentanol,n-butanol =
,
=
K neopentanol K n-butanol
K 1- pentanol pentanol K n-butanol
=
=
1.02 0.86
0.42
= 1.18
= 0.48
0.86
With excel calculation (goal seek) we found T dew =113.66 oC
Calculation of Temperature, K-values & Relative Volatilities for the Top Product
Dew point temperature for top Dew point temperature for the top was assumed as 90 oC. All calculations was done by c
using this temperature in excel. However
∑
xi =
i =1
c
yi
∑ K i =1
= 1.00 value could not be obtained.
i
o
So the dew point temperature was calculated as 96.84 C by using “Goal Seek” method in Excel and shown below. Ki = yi / xi yi
∑ x = ∑ K = 1.00 i
i
i
i
B log P = A−sat T in C; P oin mmHg ( A, B an a nd C c on onstants we w ere sh s hown in in Ta Table 2) T + C Tdew = 96.84 o C t
(top stream)
= P 760 mmHg
log
7.87863sa−t methanol =P
1473.11 96.8 96.84 4 + 230 230
;
=P2352.49sat
methanol
For other components see in Table 5.
- 22 -
mmHg
K i =
sat
Pi
K ethanol =
sat P ethanol 1517.50
=
Pt
K n-butanol =
αi =
K methanol =
,
Pt
760
sat P n-butanol
Pt
K i
P t
342.30 760
K ethanol K n-butanol
α n-butanol ,n-butanol =
=
K n-butanol K n-butanol
=
2352.49
2 0.45
=
760
K 1-pentanol =
K methanol
=
K
= 4.43 ,
0.45 0.45
=1
= 3.1
K neopentanol =
,
= 0.45 ,
HK
α ethanol ,n-butanol =
sat
=2
α methanol,n-butanol =
,
K
=
P methanol
,
sat P neopentanol
P t
P 1 sat − pentanol
=
=
P t
417.46 760
156.67 760
= 0.55
= 0.21
3.10
= 6.87 0.45 n -butanol α neopentanol,n-butanol =
K neopentanol K n-butanol
K 1-pentanol
α 1- pentanol,n-butanol =
K n-butanol
=
=
0.55 0.45
0.21 0.45
= 1.22
= 0.46
0
With excel calculation (goal seek) we found T dew =96.84 C
Calculation of Temperature, K-values & Relative Volatilities for the Bottom Product
Bubble point temperature for bottom Bubble point temperature for the top was assumed as 120 oC. All calculations was c
done by using this temperature in excel. However
c
∑ y = ∑ x K = 1.00 value could not be i
i =1
i
i
i =1
obtained. So the bubble point temperature was calculated as 122.39 oC by using “Goal Seek” method in Excel and shown below. Ki = yi / xi
∑ y = ∑ x K = 1.00 i
i
i
i
i
sat B log P = A− T in C; P oin mmHg ( A, B an a nd C c on onstants w er ere sh s hown in in Ta Table 2) T + C
Tbubble = 122.39 o C t
= P 760
log
methanol
(bottom stream)
mmHg at =P7.87863s−
1473.11 122. 122.39 39 + 230 230
;
=P4991.92sat
methanol
For other components see in Table 5.
- 23 -
mmHg
K i =
sat
Pi
K ethanol =
sat P ethanol
K n-butanol =
αi =
K i K
K methanol =
,
Pt
=
Pt
3487.52 760
sat P n-butanol
P t ,
=
P methanol P t
894.23 760
K n-butanol
α n-butanol ,n-butanol =
=
K n-but anol K n-butanol
760
4.59
=
K 1-pentanol =
K methanol
=
K
= 3.90 ,
1.18
1.18 1.18
=1
= 6.57 K neopentanol =
,
= 1.18 ,
α methanol,n-butanol =
K ethanol
=
4991.92
= 4.59
HK
α ethanol ,n-butanol =
sat
,
sat P neopentanol 1039.42
=
P t
P 1 sat − pentanol P t
=
760
440.62
= 1.37
= 0.58
760
6.57
= 5.58 1.18 n -butanol α neopentanol,n-butanol = α 1- pentanol,n-butanol =
K neopentanol K n-butanol
K 1- pentanol pentanol K n-butanol
=
=
1.37 1.18
0.58 1.18
= 1.16
= 0.49
With excel calculation (goal seek) we found T bubble =122.39 0C
Calculation of Average Relative Volatilities
α average ,i = 3 α top ,i × α bottom ,i × α feed ,i
,
α methan ol = 3 5.95 × 6.87 × 5.58 = 6.11
α ethanol = 3 4.05 × 4.43 × 3.9 = 4.12
,
3 α neopentanol = 1.18 ×1.22 ×1.16 = 1. 1.19
α n-butanol = 3 1×1×1 = 1
,
α 1- pentanol = 3 0.48 × 0.46 × 0.49 = 0.48
N min =
Calculation of Minimum Number of Plates by Using Fenske Equation
x x log LK, D × HK, W x HK, D x LK, W log α LK, avg
;
N min =
0.373 3 0.39 0.391 1 0.37 × 0.012 2 0.03 0.034 4 0.01 = 34.33
log
log 1.19
Calculation of q-Parameter
We used saturated vapor for the feed stream; so q-parameter must be taken as zero (q=0).
- 24 -
Calculation of θ -Parameter -Parameter
c
α i , ave × x f ,i
i =1
α i ,ave − θ
∑
α met ,ave × fx,met α met ,ave − θ
6.11× 0.15 6.11 − θ
= 1− q ,
+
α eth ,ave × fx,eth α eth ,ave − θ
4.12 × 0.25
+
4.12 − θ
+
< θ < α
α
HK
+
LK
α neo ,ave × fx,neo α neo ,ave − θ
1.19× 0.25 1.19 − θ
+
+
1× 0.15 1−θ
α n−but ,ave × fx,n−but α n−but ,ave − θ
+
0.48 × 0.2 0.20 0.48 − θ
+
α 1− pent ,ave × fx,1− pent α1− pent ,ave − θ
− 1+ q = 0
− 1+ 0 = 0
θ = 1.075
Calculation of Minimum Reflux Ratio, R Dmin by Using Underwood Equation
c
α ir × xD ,i
i =1
α ir − θ
∑
R D min =
6.11× 0.231
6.11 − 1.075 = 3.577
R D min
4.12 × 0.377 4.12 − 1.075
1.19 × 0.373 1.19 −1.075
* β 1 = 3.577 *1 *1.5 = 5. 5.366
=R
mDin
* β 2 = 3.577*1. 7*1.8 = 6.43 6.439 9
=R
mDin
* β 3 = 3.577 * 2. 2.4 = 8. 8.585
R
Dactual
R
Dactual
+
1 × 0.012 1 −1.075
+
0.48 ×0.006 0.48 −1.075
−1= 0
Calculation of Actual Plate Number by Using Gilliand Correlation
R - R Dmin R+1
=
5.36 5.366 6 − 3.57 3.577 7 5.366 .366 + 1
Y = 1 − exp 1.490 + 0.315 X −
Y=
+
mDin
Dactual
+
=R
R
X =
= R D min + 1
N − Nmin N + 1
= Nactual N=
⇒ N =
= 0.281
1.805 = − + × − = 0.376 1 e x p 1 . 4 9 0 0 . 3 1 5 0 . 2 8 1 0.1 (0.281)
1.805
X 0.1
Y + Nmin
1 − Y 0.37 0.376 6 + 34.3 34.33 3 1 − 0.37 .376
= 56
plates
For other reflux ratios, the calculated values were tabulated in Table 8. - 25 -
Calculation of N R and N S for the Feed Location by Using Kirk Bridge Method
W x N R f . HK xb , LK log = 0 . 2 0 6 l o g = D xf , LK xd , HK NS N R
= 1.25
N S
N S =
N R= N ac− t N S
,
N act 56 = = 25 N R 1.25 + 1 +1 N S
= 5.366 = R
λave ,top =
N R = 56 − 25 = 31
,
L= G+W L
c
∑λ
i
G = L+ D
yi and λave ,bottom =
q=0=
,
y
i
i
kmol h
× 38.914
,
L − 341.25 100
G = L − W = 341.25 − 36.4
,
1h 1 000 mol kJ × × = 4376.1 kJ s ( kW ) 1 kmol mol 3600 s
Qr = 304.85
kmol h
,
G = 304.85 kmol / h
* 43.836
1h 1 000 mol kJ × × = 3712.1 kJ s ( kW ) 1 kmol mol 3600 s
Calculation of Column Diameter and Height N
∑ MW * y i
i =1 Wmethanol
results see in Table 7 ) ∑ λ x ( for re
Qr = G * λ ave ,bottom
MW =
c
Qc = 404.85
,
L = L = 341.25
km/ol h
G = 341.25 + 63.6 = 404.85 kmol / h
Qc = G * λ ave ,top
F
D
i =1
,
L−L
L
=L341.25
,
63.6
R D =
,
i =1
q=
Calculation of Condenser and Reboiler Loads, Q c and Q r
F=W+ D ,
D
2 36.4 0.15 0.034 2 = 0.206 log 63.6 0.25 0.012 = 0.09691
=
x
methanol
Wi
K
yWi = xi K i
,
methanol
= 0.008 × 6.57 = 0.054
(
for other components see Tabl9e)
MW = (32. (32.04*0.0 04*0.054 54)) + (46.0 (46.07* 7* 0.12 0.126) 6) + (88. (88.15*0.0 15*0.047 47)) + (74.1 (74.122*0.4 22*0.461 61)) + (88. (88.15*0.3 15*0.312 12)) = 73.3 73.34 4 kg / kmol W = MV * W = 73.34
kg kmol
× 36.4
kmol h
×
1h 3600 s
= 0.742 kg s
P× MW = ρ × R× T
- 26 -
P× MW
ρ vap = ρ liq =
=
R × T c
∑ ρ x
i i
1× 73.3 73.34 4 0.082 0.082 × (122.39 122.39 + 273.15 273.15))
= 2.261 kg m3
= 791.8 91.8× 0.008 .008 + 789 789 × 0.027 .027 + 812 × 0.034 .034 + 809. 809.8 8 × 0.3 0.391 + 814.4 14.4 ×0.53 0.538 8
i =1
= 811.63 kg m3 ρ − ρ v uv = ( −0.171* l + 0.27 * l t − 0.047 )* l ρ v
1/2
2 t
811.63 3 − 2.261 2.261 811.6 uv = ( −0.17 .171*0.5 1*0.5 + 0.27* .27* 0.5 − 0.047 .047 )* 2.261 2
4W
D c =
πρv uv
=
4 × 0.742 π × 2.261× 0.856
= 0.698 m ,
1/2
= 0.856 m s
Hc = t l× ( N+ 1) = 0.5 × (56 + 1) = 28.3 m
For other reflux ratios the r esults were in Table 9.
6.2 Real 6.2 Real System (Non-Ideal) For Feed Stream Dew point temperature for the feed was assumed as 100 oC. All calculations was done by
using this temperature in excel. However P t ×
c
yi
∑ γ P i =1
*
i
= 1.00 value could not be obtained. So
i
o
the dew point temperature was calculated as 106.6 C (379.75 K) by using “Goal Seek” method in Excel and shown below.
Tr ,i = Tr ,1 = Tr , 4 =
T
, T [ K ] , Tc [ K ]
T c ,i
379.75 512.58 379.75 562.93
= 0.741 , Tr ,2 = = 0.675 , T r ,5 =
379.75 516.25 379.75 586.15
= 0.736 , T r ,3 =
379.75 550.00
= 0.690
= 0.648
α SRK ,i = 1 + ( 0.480 + 1.574ωi − 0.176ω i2 ) (1 − T r1,i2 )
2
Tc ,i , ω i wer were take taken n in Refe Referrence ence 2 and and tabu tabula late ted d in Tab Table 10 2
α SRK ,1 = 1 + ( 0.480 + 1. 1.574 × 0. 0.566 − 0.176 × 0. 0.566 2 ) (1 − 0. 0.7411 2 ) = 1.400 2
α SRK ,2 = 1 + ( 0.480 + 1.574 × 0.637 − 0.176 × 0.637 2 ) (1 − 0.736 1 2 ) = 1.442
2
α SRK ,3 = 1 + ( 0.480 + 1. 1.574 × 0. 0.604 − 0.176 × 0. 0.604 2 ) (1 − 0. 0.690 1 2 ) = 1.515
2
α SRK ,4 = 1 + ( 0.480 + 1. 1.574 × 0. 0.595 − 0 .1 .176 × 0. 0.595 2 ) (1 − 0. 0.675 1 2 ) = 1.542 2
α SRK ,5 = 1 + ( 0.480 + 1. 1.574 × 0. 0.594 − 0.176 × 0. 0.594 2 ) (1 − 0. 0.648 1 2 ) = 1.598
- 27 -
ai = ψ
2 α i R T c ,i
P c ,i
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm 3bar molK
,
ψ was taken taken in Refer Referenc encee 2 and tabul tabulate ated d in Table Table 10 a1 = 0.42748 × a2 = 0.42748 × a3 = 0.42748 × a4 = 0.42748 × a5 = 0.42748 ×
bi = Ω
RT c ,i P c ,i
,
1.40 1.400 0 × 83.1 83.14 4 2 × 512. 512.58 58 80.96 1.44 1.442 2 × 83.1 83.14 4 2 × 516. 516.25 25 63.84 1.515 1.515 × 83.14 83.142 × 550.00 38.80 1.54 1.542 2 × 83.1 83.14 4 2 × 562. 562.93 93 44.13 1.59 1.598 8 × 83.1 83.14 4 2 × 586. 586.93 93 38.80
= 1.34 ×10 7 = 1.78 ×10 7 3.49 ×107 = 3.49
= 3.27 ×10 7 = 4.18 ×10 7
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm3bar molK
Ω was taken taken in Refe Referen rence ce 2 and tabul tabulate ated d in Table Table 10 83.14 83.14 × 512.58 512.58 = 45.61 b1 = 0.08664 × b2 = 0.08664 × b3 = 0.08664 × b4 = 0.08664 × b5 = 0.08664 × β i ≡ β1 = β3 = β 5 =
bi P
,
80.96 83.14 83.14 × 516.25 516.25 63.84 83.14 83.14 × 550.00 550.00 38.80 83.14 83.14 × 562.93 562.93 44.13 83.14 83.14 × 586.15 586.15 38.80
= 58.25 = 102.11 = 91.89 = 108.82
3 T [ K ] , P [bar ] , R = 83.14 cm bar molK
RT 45.61×1.013
83.14 × 379.75 102.11×1.013 83.14 × 379.75 108.82 108.82 ×1.013 1.013 83.14 83.14 × 379.75 379.75
= 0.00146 , β 2 = = 0.00328 , β 4 =
58.25 ×1.013 83.14 × 379.75 91.89 ×1.013 83.14 × 379.75
= 0.00349
- 28 -
= 0.00187 = 0.00295
qi ≡ q1 ≡ q3 ≡
ai
,
bi RT
T [ K ] , R = 83.14 cm 3bar molK
1.34 ×10 7 45.61× 83.14 × 379.75
= 9.321
3.49 ×10 7 102.11 × 83.14 × 379.75
, q2 ≡
= 10.829 , q4 ≡
1.78 ×10 7 58.25 × 83.14 ×379.75 3.27 ×10 7 91.89 ×83.14 ×379.75
= 9.672 = 11.281
4.18 4.18×107
q5 ≡
= 12.166 108. 108.82 82 × 83.1 83.14 4 × 3 79.75 Z iv − β i v Z i = 1 + β i − qi β i ( Z iv + εβi ) ( Z iv + σβi ) 0 = 1 + 0.0 0.00146 0146 − 9.32 .321 × 0.00 0.0014 146 6
Z iv − 0.00146
( Z
v i
+ 0 × 0.00146 ) ( Z + 1 × 0.00146 ) v i
− Z iv
Ziv valu valuee for for met metha hano noll was was calc calcul ulat ated ed as as 0.987 by abov abovee equa equati tion on from from Goal Goal Seek Seek in Exce Excel l And And for for the the oth other er comp compon onen ents ts, Z iv values were tabulated in Table 14, 14, 21, 21, 28. I = v i
I1v = I 3v = I 5v =
1 σ −ε 1 1− 0 1 1− 0 1 1− 0
ln
ln ln ln
Z iv + σβ i Z iv + εβ i
0.9870 + 1 × 0.00146 0.9870 + 0 0.9649 + 1 × 0.00328 0.9649 + 0 0.95 0.9572 72 + 1× 0.00 0.0034 349 9 0.9572 + 0
= 0.00148 ,
I 2v =
= 0.00339 ,
I 4v =
1 1−0 1 1−0
ln ln
0.9826 +1 × 0.00187 0.9826 + 0 0.9670 +1 × 0.00295 0.9670 + 0
= 0.00190 = 0.00304
= 0.00364
Φ iv = exp Ziv − 1 − ln ( Ziv − β i ) − qi Iiv Φ1v = exp 0.9 0.987 870 0 − 1 − ln ( 0.9 0.98 870 − 0.0 0.00146 0146 ) − 9.321 .321 ×0.00 0.0014 148 8 = 0.988 .988 ln Φ iv = Ziv − 1 − ln ( Ziv − βi ) − qi Iiv
;
Φ 2v = exp 0. 0.9826 − 1 − ln ( 0. 0.9826 − 0.00186 ) − 9.672 × 0.00190 = 0.984 Φ 3v = exp 0.964 0.00339 = 0.968 .9649 9 − 1 − ln (0.96 0.9649 49 − 0.0 0.00328) − 10.829 × 0.0 Φ 4v = exp 0.96 0.9670 70 −1 − ln ( 0.9 0.967 670 0 − 0.002 .00295 95 ) −11.28 1.281 1 × 0.0 0.00304 0304 = 0.9 0.970 Φ 5v = exp 0.9 0.957 572 2 − 1 − ln ( 0.9 0.95 572 − 0.0 0.00349 0349 ) −12.16 2.166 6 × 0.003 .00364 64 = 0.961 .961 Z=
l i
i
β+ ( Z+
εi β) (
l i
0 = 0.00146 + (
l i
1 + β i − Z il Z+ σi β) qi β i
l i
+Z0 × 0.00146 ) (
l i
1 + 0.00 0.0014 146 6 − Z il +Z 1 × 0.00146 ) − × 9.321 9.3 21 0.0014 0.0 0146 6
l i
Z
Zil valu alue for for meth ethanol anol was was calc calcu ulate lated d as as 0.00157 by above bove equ equatio ation n fro from Goal Goal Seek Seek in Exc Excel component entss , Z il values values were were tabu tabulate lated d in Table Table 14, 21, 28. And And for the the other other compon
- 29 -
I = l i
I1l = I 3v = I 5v =
1 σ −ε 1 1− 0 1 1− 0 1 1− 0
ln
ln ln ln
Z il + σβ i Z il + εβi
0.00157 + 1 × 0.00146 0.00157 + 0 0.00395 + 1× 0.00328 0.00395 + 0 0.00 0.0037 370 0 + 1 × 0.00 0.0034 349 9
= 0.660 ,
I 2l =
= 0.604 ,
I 4v =
1 1−0 1 1−0
ln
0.00215 +1 × 0.00187
ln
= 0.625
0.00215 + 0 0.00345 +1 × 0.00295
= 0.618
0.00345 + 0
= 0.665
0.00370 + 0
Φ il = exp Zil − 1 − ln ( Zil − β i ) − qi Iil Φ1l = exp 0. 0.00157 −1 − ln ( 0. 0.00157 − 0.00146 ) − 9.321 × 0.660 = 7.605 ln Φ li = Zil − 1 − ln ( Zil − βi ) − qi Iil
;
Φ l 2 = exp 0.002 .00215 15 −1 − ln (0.0 0.00215 215 − 0.001 .00186 86 ) − 9.672 .672 × 0.625 .625 = 3.078 .078 Φ l 3 = exp 0.0 0.604 = 0.791 0.00395 395 −1 − ln (0.00 0.0039 395 5 − 0.0 0.0 0328 ) − 10.829 × 0.6 Φ l 4 = exp 0.003 .00345 45 −1 − ln ( 0.0 0.00 0345 345 − 0.002 .00295 95 ) −11.2 1.281 ×0.6 0.618 = 0.693 .693 Φ l 5 = exp 0. 0.0037 00370 0 −1 − ln ( 0.0 0.003 037 70 − 0.00 .00349 349 ) −12.16 2.166 6 ×0.6 0.665 = 0.545 .545
i
3
Φ l i = v K Φi =K
αi =
,
0.791 0.968 K i
K
1
yi
3
=x
K i 0.25 0.82
0.988
=K
4
= 7.70 , 0.693
HK
K ethanol K n-butanol
,
K n-butanol K n-butanol 1
=x
= 0.306 ,
fi v = yi Φ iv P ,
=
3.13 0.71
=
0.15 7.70 4
K methanol
=
K
0.71
=1
= 0.019 , 0.15 0.71
= K
3.078 = 3.13 0.984
,
=K
5
0.545 0.961
= 0.57
7.70
= 10.78 0.71 n -butanol
= 4.38 ,
0.71
=x
2
= 0.71 ,
0.970
α methanol,n-butanol =
,
α n-butanol ,n-butanol =
=x
7.605
= 0.82 ,
α ethanol ,n-butanol =
i
= K
α neopentanol,n-butanol = α 1- pentanol,n-butanol =
2
=x
= 0.210 ,
0.25 3.13 5
K neopentanol K n-butanol
K 1- pentanol pentanol K n-butanol
=
=
0.71
0.57 0.71
= 0.08
=x
0.20
0.57
= 0.352
f1v = 0 .15 × 0.988 ×1.013 = 0. 0.1501
f 2v = 0.25 × 0.9 0.984 × 1. 1.013 = 0.2491 ,
f 3v = 0.25 ×0. 0.968 ×1. 1.013 = 0.2451
f 4v = 0.15 × 0. 0.970 × 1. 1.013 = 0.1474
f 5v = 0.20 ×0. 0.961 ×1.013 = 0.1947
fi l = xi Φ il Pt ,
0.82
,
f1l = 0 .019 × 7.605 ×1.013 = 0.1501
f 2l = 0.08 × 3. 3.078 ×1.013 = 0.2491 ,
f 3l = 0.306 ×0.7 0.791 ×1.013 = 0.2451
f 4l = 0.21× 0.693 ×1.013 = 0.1474
f 5l = 0.352 ×0. 0.545 ×1.013 = 0.1947
,
- 30 -
= 1.14
= 0.79
In Vapor-Liquid Equilibrium, fugacity of liquid and vapor must be equal to each other. So, our results support this condition. ( f i l = f i v ) B log P = A−sat T in C; P oin mmHg ( A, B an a nd C constants w er ere sh s hown in in Ta Table1) T + C Tdew = 106.6 o C t
= P 760
log
methanol
( feed stream)
mmHg
= 7P.87863sa−t
1473.11 106.6 + 230
3178.72sat =P
;
1 atm
× mmHg
methanol
760 mmHg
×
1.013 bar 1 atm
= 4.237
17, 24, 24, 31. 31. For ot her components see in Table 17,
yi Φ P = xi γ i Pi , *
v i t
γ1 = γ3 = γ 5 =
γ i =
0.15 × 0.988 ×1.013 0.019 × 4.237 0.25 × 0.968 ×1.013 0.306 × 0.804 0.20 0.20 × 0.96 0.961 1 ×1.01 1.013 3 0.352 × 0.31 0.317 7
yi Φiv P t xi P i *
= 1.818 ,
γ 2 =
= 0.997 ,
γ 4 =
0.080 × 2.822 0.25 × 0.970 ×1.013
= 1.105
0.210 × 0.672
= 1.044
= 1.741
With excel calculation (goal seek), P t ×
yi
∑ γ P
sat
i
0.15 × 0.984 ×1.013
i
= 1.00 we found T dew =106.6 oC
i
For Top Product
Dew point temperature for the feed was assumed as 90 oC. All calculations was done by using this temperature in excel. However P t ×
c
yi
∑ γ P i =1
sat
i
= 1.00 value could not be obtained.
i
So the dew point temperature was calculated as 96.98 oC (370.13 K) by using “Goal Seek” method in Excel and shown below.
Tr ,i = Tr ,1 = Tr , 4 =
T T c ,i
, T [ K ] , Tc [ K ]
370.13 512.58 370.13 562.93
= 0.722 , Tr ,2 = = 0.658 , T r ,5 =
370.13 516.25 370.13 586.15
= 0.717 , T r ,3 = = 0.631
- 31 -
370.13 550.00
= 0.673
bar
α SRK ,i = 1 + ( 0.480 + 1.574ωi − 0.176ω i2 ) (1 − T r1,i2 )
2
Tc ,i , ω i wer were take taken n in Refer eferen ence ce 2 and and tabu tabula late ted d in Tab Table 10 2
α SRK ,1 = 1 + ( 0.480 + 1. 1.574 × 0. 0.566 − 0.176 × 0. 0.566 2 ) (1 − 0. 0.722 1 2 ) = 1.434 2
α SRK ,2 = 1 + ( 0.480 + 1.574 × 0.637 − 0.176 × 0.637 2 ) (1 − 0.717 1 2 ) = 1.479
2
α SRK ,3 = 1 + ( 0.480 + 1. 1.574 × 0. 0.604 − 0.176 × 0. 0.604 2 ) (1 − 0. 0.6731 2 ) = 1.551
2
α SRK ,4 = 1 + ( 0.480 + 1. 1.574 × 0. 0.595 − 0 .1 .176 × 0. 0.595 2 ) (1 − 0. 0.658 1 2 ) = 1.578 2
α SRK ,5 = 1 + ( 0.480 + 1. 1.574 × 0. 0.594 − 0.176 × 0. 0.594 2 ) (1 − 0. 0.6311 2 ) = 1.633 ai = ψ
α i R 2T c ,i P c ,i
,
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm 3bar molK
taken in Refer Referenc encee 2 and tabul tabulate ated d in Table Table 10 ψ was taken a1 = 0.42748 × a2 = 0.42748 × a3 = 0.42748 × a4 = 0.42748 × a5 = 0.42748 ×
bi = Ω
RT c ,i P c ,i
,
1.43 1.434 4 × 83.1 83.14 4 2 × 512. 512.58 58 80.96 1.47 1.479 9 × 83.1 83.14 4 2 × 516. 516.25 25 63.84 2 1.551 1.551× 83.14 83.14 × 550.00
38.80 1.57 1.578 8 × 83.1 83.14 4 2 × 562. 562.93 93 44.13 1.63 1.633 3 × 83.1 83.14 4 2 × 586. 586.93 93 38.80
= 1.38 ×10 7 = 1.82 ×10 7 3.57 ×107 = 3.57
= 3.35 ×10 7 = 4.27 ×10 7
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm3bar molK
Ω was taken taken in Refe Referen rence ce 2 and tabul tabulate ated d in Table Table 10 83.14 83.14 × 512.58 512.58 = 45.61 b1 = 0.08664 × b2 = 0.08664 × b3 = 0.08664 × b4 = 0.08664 × b5 = 0.08664 ×
80.96 83.14 83.14 × 516.25 516.25 63.84 83.14 83.14 × 550.00 550.00 38.80 83.14 83.14 × 562.93 562.93 44.13 83.14 83.14 × 586.15 586.15 38.80
= 58.25 = 102.11 = 91.89 = 108.82
- 32 -
β i ≡ β1 = β3 = β 5 =
qi ≡ q1 ≡ q3 ≡
bi P
T [ K ] , P [bar ] , R = 83.14 cm3bar molK
,
RT 45.61×1.013
83.14 × 370.13 102.11×1.013 83.14 × 370.13 108.82 108.82 ×1.013 1.013 83.14 83.14 × 370.13 370.13
ai
,
bi RT
= 0.00150 , β 2 = = 0.00336 , β 4 =
58.25 ×1.013
= 0.00192
83.14 × 370.13 91.89 ×1.013
= 0.00302
83.14 × 370.13
= 0.00358
T [ K ] , R = 83.14 cm 3bar molK
1.38 ×10 7 45.61× 83.14 × 370.13
= 9.798
3.57 ×10 7 102.11 × 83.14 × 370.13
, q2 ≡
= 11.373 , q4 ≡
1.82 ×10 7 58.25 ×83.14 ×370.13 3.35 ×10 7 91.89 ×83.14 ×370.13
= 10.181 = 11.840
4.27 4.27 ×107
q5 ≡
= 12.758 108.82 108.82 × 83.14 83.14 × 370.13 Z iv − β i v Zi = 1 + β i − qi β i ( Ziv + εβi ) ( Z iv + σβi ) 0 = 1 + 0.00 .00150 150 − 9.798 .798 × 0.00 .00150 150
Z iv − 0.00150
( Z
v i
+ 0 × 0.00150 ) ( Z + 1 × 0.00150 ) v i
− Z iv
v
Zi valu valuee for for meth methan anol ol was was calc calcul ulat ated ed as as 0.988 by abov abovee equa equati tion on from from Goal Goal Seek Seek in Exce Excel l 13, 20, 20, 27. 27. And And for the other other com compon ponen ents ts, Z iv values were tabulated in Table 13, I = v i
I1v = I 3v = I 5v =
1 σ −ε 1 1− 0 1 1− 0 1 1− 0
ln
ln ln ln
Z iv + σβ i Z iv + εβ i
0.9880 + 1 × 0.00150 0.9880 + 0 0.9659 + 1 × 0.00336 0.9659 + 0 0.95 0.9575 75 + 1× 0.00 0.0035 358 8 0.9575 + 0
= 0.00152 ,
I 2v =
= 0.00347 ,
I 4v =
1 1−0 1 1−0
ln ln
0.9828 +1 × 0.00192 0.9828 + 0 0.9673 +1 × 0.00302 0.9673 + 0
= 0.00373
Φ iv = exp Ziv − 1 − ln ( Ziv − β i ) − qi Iiv Φ1v = exp 0. 0.9880 − 1 − ln ( 0. 0.9880 − 0.00150 ) − 9.798 × 0.00152 = 0.987 ln Φ iv = Ziv − 1 − ln ( Ziv − βi ) − qi Iiv
;
Φ 2v = exp 0.98 0.9828 28 − 1 − ln ( 0.9 0.98 828 − 0.00 .00192 192 ) −10.1 10.181 81 ×0.00 0.0019 195 5 = 0.982 .982 Φ 3v = exp 0.965 .9659 9 − 1 − ln (0.96 0.9659 59 − 0.0 0.00 336 ) − 11.373 × 0.0 0.00347 = 0.965 Φ 4v = exp 0.96 .9673 −1 − ln ( 0.9 0.967 673 3 − 0.00 0.0030 302 2 ) −11.8 11.840 40 × 0.00 0.0031 312 2 = 0.9 0.967 Φ 5v = exp 0.9 0.957 575 5 −1 − ln ( 0.9 0.957 575 5 − 0.003 .00358 58 ) −12.7 12.75 58 × 0.00 .00373 373 = 0.95 0.958 8
- 33 -
= 0.00195 = 0.00312
Z=
l i
i
β+ ( Z+
εi β) (
l i
0 = 0.00150 + (
l i
1 + β i − Z il Z+ σi β) qi β i
l i
+Z0 × 0.00150 ) (
l i
1 + 0.00 0.0015 150 0 − Z il +Z 1 × 0.00150 ) − × 9.798 9.7 98 0.0015 0.0 0150 0
l i
Z
Zil valu alue for for meth ethanol anol was was calc calcu ulate lated d as as 0.00187 by above bove equ equatio ation n fro from Goal Goal Seek Seek in Exc Excel And And for the the other other compon component entss , Z il values values were were tabu tabulate lated d in Table Table 14, 21, 28. I = l i
I1l = I 3v = I 5v =
1 σ −ε 1 1− 0 1 1− 0 1 1− 0
ln
ln ln ln
Z il + σβ i Z il + εβ i
0.00187 + 1 × 0.00150 0.00187 + 0 0.00426 + 1 × 0.00336 0.00426 + 0 0.00 0.0043 430 0 + 1 × 0.00 0.0035 358 8
= 0.590 ,
I 2l =
= 0.582 ,
I 4v =
1 1−0 1 1−0
ln
0.00255 +1 × 0.00192
ln
= 0.560
0.00255 + 0 0.00385 +1 × 0.00302
= 0.580
0.00385 + 0
= 0.606
0.00430 + 0
Φ il = exp Zil − 1 − ln ( Zil − β i ) − qi Iil Φ1l = exp 0. 0.00187 −1 − ln ( 0. 0.00187 − 0.00150 ) − 9.798 × 0.590 = 3.108 ln Φ li = Zil − 1 − ln ( Zil − βi ) − qi Iil
;
Φ l 2 = exp 0.0 0.002 0255 55 −1 − ln ( 0.0 0.00 0255 255 − 0.001 .00192 92 ) −10.1 10.181 81 ×0.560 .560 =1.93 .935 Φ l 3 = exp 0.0 0.00426 426 −1 − ln (0.0 0.00426 0426 − 0.00336 ) − 11.373 × 0.5 0.582 = 0.551 Φ l 4 = exp 0.0 0.003 0385 85 −1 − ln ( 0. 0.0038 00385 5 − 0.0 0.0030 0302 ) −11.8 11.840 40 ×0.58 .580 = 0.467 .467 Φ l 5 = exp 0. 0.0043 00430 0 −1 − ln ( 0.0 0.00 0430 430 − 0.00 .00358 ) −12.7 12.758 58 × 0.606 .606 = 0.22 0.226 6
i
3
Φ l i = v K Φi =K
αi =
0.551 0.965 K i
K
,
1
= K
3.108 0.987
= 0.57 ,
,
α ethanol ,n-butanol =
= 3.15 ,
4
=K
0.467 0.967
α methanol,n-butanol = HK
K ethanol K n-butanol
α n-butanol ,n-butanol =
=
K n-but anol K n-butanol
1.97 0.48
=
2
=
K
= 4.08 ,
0.48
1.935
= 1.97 0.982
= 0.48 ,
K methanol
0.48
= K
=1
,
5
=K
0.226 0.958
= 0.24
3.15
= 6.52 0.48 n -butanol α neopentanol,n-butanol = α 1- pentanol,n-butanol =
- 34 -
K neopentanol K n-butanol
K 1- pentanol pentanol K n-butanol
=
=
0.57 0.48
0.24 0.48
= 1.18
= 0.49
yi
i
=x
3
=x
,
K i 0.373 0.57
=x
1
0.231 3.15
0.012
= 0.655 ,
fi v = yi Φ iv P ,
= 0.073 ,
4
=x
0.48
2
=x
0.377 1.97
= 0.192 0.006
= 0.024 ,
5
=x
0.24
= 0.027
f1v = 0 .231× 0.987 ×1.013 = 0.2310
f 2v = 0.377 × 0.982 ×1. 1.013 = 0.3755
,
f 3v = 0.373 ×0. 0.965 ×1. 1.013 = 0.3651
f 4v = 0.012 × 0.9 0.967 × 1. 1.013 = 0.0116
,
f 5v = 0.006 ×0.9 0.958 ×1.013 = 0.0061
fi l = xi Φ il Pt ,
f1l = 0 .073 × 3.108 ×1.013 = 0.2310
f 2l = 0.192 ×1.935 ×1.013 = 0.3755
,
f 3l = 0.655 ×0.5 0.551 ×1.013 = 0.3651
f 4l = 0.024 × 0.4 0.467 ×1. 1.013 = 0.0116
,
f 5l = 0.027 × 0.226 ×1. 1.013 = 0.0061
In Vapor-Liquid Equilibrium, fugacity of liquid and vapor must be equal to each other. So, our results support this condition. ( f i l = f i v )
B log P = A−sat T in C; P oin mmHg ( A, B an a nd C constants we w ere sh s hown in in Ta Table1) T + C Tdew = 96.98 o C t
= P 760
log
(top stream)
mmHg
methanol
= 7P.87863sa−t
1473.11
= 2P362.78sa9t
;
96.98 + 230
methanol
1 atm
× mmHg
760 mmHg
×
1.013 bar 1 atm
17, 24, 24, 31. 31. For ot her components see in Table 17,
yi Φ P = xi γ i Pi v i t
γ1 = γ3 = γ 5 =
sat
,
γ i =
0.231× 0.987 ×1.013 0.073 × 3.149 0.373 × 0.965 ×1.013 0.655 × 0.559 0.00 0.006 6 × 0.95 0.958 8 ×1.01 1.013 0.02 0.027 7 × 0.21 0.210 0
yi Φiv P t xi P i sat
=1 ,
γ 2 =
= 0.997 ,
0.377 × 0.982 ×1.013
= 0.964 0.192 × 2.032 0.012 × 0.967 ×1.013 γ 4 = = 1.031 0.024 × 0.459
= 1.089
With excel calculation (goal seek), P t ×
yi
∑ γ P
sat
i
i
i
- 35 -
= 1.00 we found T dew =96.98 oC
= 3.149
ba
For Bottom Product Bubble point temperature for the feed was assumed as 120 oC. All calculations was done
c
∑ x γ P i
by using this temperature in excel. Howeveri =1
i
sat i
= 1.00
P t
value could not be obtained.
So the bubble point temperature was calculated as 128.5 oC (401.65 K) by using “Goal Seek” method in Excel and shown below.
Tr ,i = Tr ,1 = Tr , 4 =
T
, T [ K ] , Tc [ K ]
T c ,i
401.65 512.58 401.65 562.93
= 0.784 , Tr ,2 = = 0.713 , T r ,5 =
401.65 516.25 401.65 586.15
= 0.778 , T r ,3 =
401.65 550.00
= 0.730
= 0.685
α SRK ,i = 1 + ( 0.480 + 1.574ωi − 0.176ω i2 ) (1 − T r1,i 2 )
2
Tc ,i , ω i were were take taken n in Refe Referrence ence 2 and tab tabulat ulated ed in Tab Table 10 2
α SRK ,1 = 1 + ( 0.480 + 1. 1.574 × 0. 0.566 − 0.176 × 0. 0.566 2 ) (1 − 0. 0.784 1 2 ) = 1.325 2
α SRK ,2 = 1 + ( 0.480 + 1.574 × 0.637 − 0.176 × 0.637 2 ) (1 − 0.778 1 2 ) = 1.361
2
α SRK ,3 = 1 + ( 0.480 + 1. 1.574 × 0. 0.604 − 0 .1 .176 × 0. 0.604 2 ) (1 − 0. 0.730 1 2 ) = 1.437 2
α SRK ,4 = 1 + ( 0.480 + 1. 1.574 × 0. 0.595 − 0 .1 .176 × 0. 0.595 2 ) (1 − 0. 0.7131 2 ) = 1.465 2
α SRK ,5 = 1 + ( 0.480 + 1. 1.574 × 0. 0.594 − 0.176 × 0. 0.594 2 ) (1 − 0. 0.685 1 2 ) = 1.520
ai = ψ
α i R 2T c ,i P c ,i
,
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm 3bar molK
taken in Refer Referenc encee 2 and tabul tabulate ated d in Table Table 10 ψ was taken a1 = 0.42748 × a2 = 0.42748 × a3 = 0.42748 × a4 = 0.42748 × a5 = 0.42748 ×
1.32 1.325 5 × 83.1 83.14 4 2 × 512. 512.58 58 80.96 1.36 1.361 1× 83.1 83.14 4 2 × 516. 516.25 25 63.84 1.437 1.437 × 83.14 83.142 × 550.00 38.80 1.46 1.465 5 × 83.1 83.14 4 2 × 562. 562.93 93 44.13 1.52 1.520 0 × 83.1 83.14 4 2 × 586. 586.93 93 38.80
= 1.27 ×10 7 = 1.68 ×10 7 3.31×107 = 3.31
= 3.11 ×10 7 = 3.98 ×10 7
- 36 -
bi = Ω
RT c ,i
,
P c ,i
Tc ,i [ K ] , Pc ,i [bar ] , R = 83.14 cm3bar molK
Ω was taken taken in Refe Referen rence ce 2 and tabul tabulate ated d in Table Table 10 83.14 83.14 × 512.58 512.58 = 45.61 b1 = 0.08664 × b2 = 0.08664 × b3 = 0.08664 × b4 = 0.08664 × b5 = 0.08664 × β i ≡ β1 = β3 = β 5 =
qi ≡ q1 ≡ q3 ≡ q5 ≡
bi P
80.96 83.14 83.14 × 516.25 516.25 63.84 83.14 83.14 × 550.00 550.00 38.80 83.14 83.14 × 562.93 562.93 44.13 83.14 83.14 × 586.15 586.15 38.80
83.14 × 401.65 102.11×1.013 83.14 × 401.65 108.82 108.82 ×1.013 1.013 83.14 83.14 × 401.65 401.65
bi RT
= 102.11 = 91.89 = 108.82
3 T [ K ] , P [bar ] , R = 83.14 cm bar molK
,
RT 45.61×1.013
ai
= 58.25
,
= 0.00138 , β 2 = = 0.00310 , β 4 =
58.25 ×1.013 83.14 × 401.65 91.89 ×1.013 83.14 × 401.65
= 0.00177 = 0.00279
= 0.00330
T [ K ] , R = 83.14 cm 3bar molK
1.27 ×10 7 45.61× 83.14 × 401.65
= 8.341
3.31×10 7 102.11 × 83.14 × 401.65
, q2 ≡
= 9.709 , q4 ≡
1.68 ×10 7 58.25 ×83.14 × 401.65 3.11 ×10 7
91.89 ×83.14 × 401.65
= 8.629
= 10.130
3.98 3.98×107
= 10.946 108. 108.82 82 × 83.1 83.14 4 × 401.65 Z iv − β i v Z i = 1 + β i − qi β i ( Ziv + εβi ) ( Z iv + σβi ) 0 = 1 + 0.001 .0013 38 − 8.341 .341× 0.00 0.001 138
Z iv − 0.00138
( Z
v i
+ 0 × 0.00138 ) ( Z + 1 × 0.00138 ) v i
− Z iv
Ziv valu valuee for for meth methan anol ol was was calc calcul ulat ated ed as 0.9892 by abov abovee equa equati tion on from from Goal Goal Seek Seek in Exce Excel l And And for for the the othe otherr compo compone nent ntss, Z iv values were tabulated in Table 13 20, 20, 27.
- 37 -
1
I = v i
σ −ε 1
I1v =
1− 0 1
I 3v =
1− 0 1
I 5v =
1− 0
ln
ln ln ln
Z iv + σβ i Z iv + εβ i
0.9892 + 1 × 0.00138 0.9892 + 0 0.9704 + 1 × 0.00310 0.9704 + 0 0.96 0.9638 38 + 1× 0.00 0.0033 330 0 0.9638 + 0
= 0.00140 ,
I 2v =
= 0.00319 ,
I 4v =
1 1−0 1 1−0
ln ln
0.9853 +1 × 0.00177
= 0.00179
0.9853 + 0 0.9721 +1 × 0.00279
= 0.00286
0.9721 + 0
= 0.00342
Φ iv = exp Ziv − 1 − ln ( Ziv − β i ) − qi Iiv Φ1v = exp 0.9 0.989 892 2 − 1 − ln ( 0.9 0.98 892 − 0.0 0.00138 0138 ) − 8.34 .341 × 0.00 0.0014 140 0 = 0.9 0.990 ln Φ iv = Ziv − 1 − ln ( Ziv − βi ) − qi Iiv
;
Φ 2v = exp 0. 0.9853 −1 − ln ( 0. 0.9853 − 0.00177 ) − 8.629 × 0.00179 = 0.987 Φ 3v = exp 0.970 .9704 4 − 1 − ln (0.97 0.9704 04 − 0.0 0.00310 ) − 9.709 × 0.0 0.00319 = 0.973 Φ 4v = exp 0.97 0.9721 21 −1 − ln (0.97 0.9721 21 − 0.0 0.00279 0279 ) −10.13 0.130 0 × 0.002 .00286 86 = 0.975 .975 Φ 5v = exp 0.9 0.963 638 8 −1 − ln (0.9 0.9638 638 − 0.003 .00330 30 ) −10.9 0.946 × 0.00 .00342 342 = 0.96 .967
Z=
l i
i
β+ ( Z+
εi β) (
l i
0 = 0.00138 + (
l i
1 + β i − Z il Z+ σi β) qi β i
l i
+ Z0 × 0.00138 ) (
l i
1 + 0.00 0.0013 138 8 − Z il +Z 1 × 0.00138 ) − × 8.341 8.3 41 0.0013 0.0 0138 8
l i
Z
Zil value alue for for metha ethan nol was was calc calcu ulate lated d as as 0.00169 by abov abovee equa equati tio on from from Goal oal See Seekk in Excel xcel And And for the the other other compon component entss , Z il values values were were tabu tabulate lated d in Table Table 14, 21, 28. I = l i
I1l = I 3v = I 5v =
1 σ −ε 1 1− 0 1 1− 0 1 1− 0
ln
ln ln ln
Z il + σβ i Z il + εβ i
0.00169 + 1× 0.00138 0.00169 + 0 0.00425 + 1 × 0.00310 0.00425 + 0 0.00 0.0042 420 0 + 1 × 0.00 0.0033 330 0 0.00420 + 0
= 0.599 ,
I 2l =
= 0.548 ,
I 4v =
1 1−0 1 1−0
ln ln
0.00245 +1 × 0.00177
= 0.567
0.00365 + 0
= 0.580
Φ il = exp Zil − 1 − ln ( Zil − β i ) − qi Iil Φ1l = exp 0.00 .00169 −1 − ln (0.00 0.0016 169 9 − 0.001 .00138 38 ) − 8.341 .341 ×0.5 0.599 = 8.223 .223 ln Φ li = Zil − 1 − ln ( Zil − βi ) − qi Iil
= 0.543
0.00245 + 0 0.00365 +1 × 0.00279
;
Φ l 2 = exp 0.002 .00245 45 −1 − ln (0.0 0.00245 245 − 0.001 .00177 77 ) − 8.629 .629 × 0.543 .543 = 4.98 .982 Φ l 3 = exp 0.0 0.00425 425 −1 − ln (0.00 0.0042 425 5 − 0.0 0.0 0310 ) − 9.709 × 0.548 = 1.576 Φ l 4 = exp 0.003 .00365 65 −1 − ln ( 0.0 0.00 0365 365 − 0.002 .00279 79 ) −10.1 10.130 30 ×0.56 .567 =1.365 .365 Φ l 5 = exp 0. 0.0042 00420 0 −1 − ln (0.0 0.0042 0420 − 0.00 .00330 330 ) −10.94 0.946 6 ×0.5 0.580 = 0.71 0.719 9
- 38 -
Φ l i K = v Φi
i
=K
3
αi =
1.576 0.973 K i
K
= 1 K
,
4
=K
1.365 0.975
α methanol,n-butanol =
,
HK
K ethanol K n-butanol
α n-butanol ,n-butanol =
3
= 8.31 ,
0.990
= 1.62 ,
α ethanol ,n-butanol =
yi = Ki xi
8.223
=
K n-but anol K n-butanol
5.05 1.40
=
= 2 K
= 1.40 ,
K methanol
=
K
= 3.60 ,
1.40 1.40
=1
,
fi v = yi Φiv P ,
4
=K
0.719
= 0.74
0.967
= 5.93 1.40 n -butanol α neopentanol,n-butanol = α 1- pentanol,n-butanol =
1
= 1y.62 × 0.034 = 0.056 ,
5
8.31
y = 8.31 × 0.008 = 0.068
,
4.982 = 5.05 0.987
K neopentanol K n-butanol
K 1- pentanol pentanol K n-butanol
=
=
1.62 1.40
0.74 1.40
= 1.16
= 0.53
y2 = 5.05 ×0.027 = 0. 0.139
,
0 .548 , = 1y.40 ×0.391 = 0.
5
= 0y.74 ×0.538 =0.400
f1v = 0 .068 × 0.99 ×1.013 = 0.0687
f 2v = 0.139 × 0.9 0.987 × 1. 1.013 = 0.1386
,
f 3v = 0.056 ×0.9 0.973 ×1.013 = 0.0548
f 4v = 0.548 × 0. 0.975 ×1.013 = 0.5415
,
f 5v = 0.400 ×0.9 0.967 ×1. 1.013 = 0.3921
fi l = xi Φ il Pt ,
f1l = 0 .008 × 8.223 ×1.013 = 0.0687
f 2l = 0.027 × 4.9 4.982 ×1.013 = 0.1386
,
f 3l = 0.034 ×1.576 ×1.013 = 0.0548
f 4l = 0.391×1.365 ×1.013 = 0.5415
,
f 5l = 0.538 ×0.7 0.719 ×1. 1.013 = 0.3921
In Vapor-Liquid Equilibrium, fugacity of liquid and vapor must be equal to each other. So, our results support this condition. ( f i l = f i v ) B log P = A−sat T in C; P oin mmHg ( A, B an a nd C constants we w ere sh s hown in in Ta Table1) T + C Tbubble = 128.5 o C t
= P 760
log
methanol
(bottom stream)
mmHg
= 7P.87863sa−t
1473.11 128.5 + 230
;
=P5881.75sa8t
methanol
17, 24, 24, 31. 31. For other components see in Table 17,
- 39 -
1 atm
× mmHg
760 mmHg
×
1.013 bar 1 atm
= 7.840
r
ba
yi Φ P = xi γ i Pi v i t
γ1 = γ3 = γ 5 =
sat
γ i =
,
0.068 × 0.99 ×1.013
yi Φ iv P t xi P i sat
= 0.015 ,
0.008 × 7.840 0.056 × 0.973 ×1.013
0.034 ×1.685 0.40 0.400 0 × 0.96 0.967 7 ×1 .013 0.538 0.538 × 0.732 0.732
γ 2 =
= 0.361 ,
0.139 × 0.987 ×1.013
= 0.036
0.027 × 5.572 0.548 × 0.975 ×1.013
γ 4 =
= 0.481
0.391 ×1.464
= 1.801 c
∑ x γ P i
i =1
With excel calculation (goal seek),
P t
α methan ol = 3 10.78 × 6.52 × 5.93 = 7.47
,
α ethanol = 3 4.38 × 4.08 × 3.60 = 4.01 , α n-butanol = 3 1×1×1 = 1
N min =
= 1.00 we found T bubble =128.5 oC
Calculation of Average Relative Volatilities
α average ,i = 3 α top ,i × α bottom ,i × α feed ,i
sat i
i
,
3 α neopentanol = 1.14 ×1.18 ×1.16 = 1. 1.16
α 1- pentanol = 3 0.79 × 0.49 × 0.53 = 0.59
Calculation of Minimum Number of Plates by Using Fenske Equation
x LK, D x HK, W × log x x H K , D L K , W
N min =
;
log α LK, avg
0.373 3 0.39 0.391 1 0.37 × 0.012 2 0.03 0.034 4 0.01 = 39.56
log
log 1.16
Calculation of q-Parameter
We used saturated vapor for the feed stream; so q-parameter must be taken as zero (q=0).
Calculation of θ -Parameter -Parameter
c
α i , ave × x f ,i
i =1
α i ,ave − θ
∑
α met ,ave × fx,met α met ,ave − θ
7.47 × 0.15 7.47 − θ
+
= 1− q ,
+
α eth ,ave × fx,eth α eth ,ave − θ
4.01× 0.25 4 .0 1 − θ
+
< θ < α
α
HK
+
LK
α neo ,ave × fx,neo α neo ,ave − θ
1.16× 0.25 1.16 − θ
+
+
1× 0.15 1−θ
α n−but ,ave × fx,n−but α n−but ,ave − θ
+
0.59 × 0.20 0.59 − θ
θ = 1.051
- 40 -
+
α 1− pent ,ave × fx,1− pent α1− pent ,ave − θ
−1+ 0 = 0
− 1+ q = 0
Calculation of Minimum Reflux, R Dmin by Using Underwood Equation
c
α ir × xD ,i
i =1
α ir − θ
∑
R D min =
7.47 × 0.231
7.47 − 1.051 = 3.516
R D min
4.01 × 0.377 4.01 −1.051
1.16 × 0.373 1 × 0.012 1.16 −1.051
* β 1 = 3.516 *1 *1.5 = 5. 5.274
=R
mDin
* β 2 = 3.516*1.8 6*1.8 = 6.32 6.328 8
=R
mDin
* β 3 = 3.516 * 2. 2.4 = 8. 8.438
R
Dactual
R
Dactual
+
1 −1.051
+
0.59 ×0.006 0.59 −1.051
−1= 0
Calculation of Actual Plate Number by Using Gilliand Correlation
R - R Dmin
=
R+1
5.27 5.274 4 − 3.51 3.516 6
N − Nmin N + 1
= Nactual N=
= 0.280
5.27 .274 + 1
Y = 1 − exp 1.490 + 0.315 X −
Y=
+
mDin
Dactual
+
=R
R
X =
= R D min + 1
⇒ N =
1.805 1 e x p 1 . 4 9 0 0 . 3 1 5 0 . 2 8 0 = − + × − = 0.376 0.1 (0.280)
1.805
X 0.1
Y + Nmin
1 − Y 0.37 0.376 6 + 39.5 39.56 6 1 − 0.37 .376
= 64
plates
For other reflux ratios, the calculated values were tabulated in Table 34.
Calculation of N R and N S for the Feed Location by Using Kirk Bridge Method
W x N R f . HK xb , LK log = 0 . 2 0 6 l o g = D x x N S f , LK d , HK N R N S
= 1.25
N S =
,
N R= N ac− t N S
N act 64 = = 28 N R 1.25 + 1 +1 N S
,
2 36.4 0.15 0.034 2 0.206 log 0.25 0.012 = 0.09691 = 6 3 . 6
N R = 64 − 28 = 36
- 41 -
Calculation of Condenser and Reboiler Loads, Q c and Q r
F=W+ D ,
D
= 5.274 = R
L = G+W L
c
∑λ
λave,top =
=L335.4
,
63.6
R D =
,
y andλave ,bottom =
i
i
Qc = G * λ ave ,top
q =0=
,
y
kmol h
× 38.914
1h 1000 mol kJ × × = 4312.9 kJ s ( kW ) 1 kmol mol 3600 s
L− 335.4 100
Qr = 299.00
,
kmol h
G = 299.00 kmol / h
,
* 43.836
1h 1000 mol kJ × × = 3640.9 kJ s ( kW ) 1 kmol mol 3600 s
N
∑ MW * y i
=
x
K
methanol
yWi = xi K i
,
Wi
methanol
(
= 0.008 × 8.31 = 0.068
for other components see Tabl3e5 )
MW = (32. (32.04*0.0 04*0.068 68)) + (46.0 (46.07* 7* 0.13 0.139) 9) + (88. (88.15*0.0 15*0.056 56)) + (74. (74.12 122* 2* 0.54 0.548) 8) + (88. (88.15*0.4 15*0.400 00)) = 89.4 89.42 2 kg / kmol
W = MV × W = 89.42
Calculation of Column Diameter and Height
i =1 Wmethanol
x ( for results see in Table33)
i
G = L − W = 335.4 − 36.4
,
Qr = G * λ ave ,bottom
MW =
i
Qc = 399.00
,
L = L = 335.4
c
G = 335.4 + 63.6 = 399.00 kmol / h
,
F
km/ol h
i =1
G = L+D
L− L
D
∑λ
i =1
q=
L
kg kmol
× 36.4
kmol h
×
1h 3600 s
= 0.904 kg s
P× MW = ρ × R× T ρ vap = ρ liq =
P× MW
=
R × T c
∑ ρ
i i
1× 89.4 89.42 2 0.082 0.082 × (128.5 128.5 + 273.15 273.15))
= 2.715 kg m3
x 0.008 = 791.8 91.8 × .008 + 789 789 × 0.02 0.027 7 + 812 × 0.03 .034 + 809 809.8 × 0.391 .391 + 814.4 14.4 ×0.53 0.538 8 = 811.6 11.63 3
i =1 1/2
ρ − ρ v uv = ( −0.171* l + 0.27 * l t − 0.047 )* l ρ v 2 t
1/2
811.63 63 − 2.71 2.715 5 811. uv = ( −0.171 .171*0. *0.5 5 + 0.27*0. 0.27*0.5 5 − 0.047 .047 )* 2.715 2
D c =
4W
πρv uv
=
4 × 0.904 π × 2.715 × 0.781
= 0.737 m ,
Hc = t l× ( N+ 1) = 0.5 × (64 + 1) = 32.5 m
For other reflux ratios the r esults were in Table 35.
- 42 -
= 0.781 m s
3
kg
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