LIQUID NITROGEN GENERATOR AND PROCESS

Abstract

A process for producing liquid nitrogen utilizes a distillation system comprising higher-pressure and lower-pressure columns, a first condenser in the lower-pressure column bottom, and a second condenser disposed on top of the lower-pressure column. Feed air is compressed in a main air compressor above 15 bar(a) and cooled in a main heat exchanger. A first cooled air portion is expanded in a cold turbine before separation in the higher-pressure column. A second cooled air portion is liquefied before entering the higher-pressure column. Liquid nitrogen streams condensed by both the first and second condensers are combined to yield the final product. Another feature involves warming and expanding a lost air stream (e.g., from the cold turbine outlet and/or higher-pressure column) to below 2 bar(a) in a warm turbine.

Claims

1. A process for production of liquid nitrogen from a system of columns comprised of a higher-pressure column, a lower-pressure column, a first condenser disposed in a bottom portion of the lower-pressure column, and a second condenser, the process comprising the steps of: purifying a feed air in a purification unit at a pressure greater than 15 bar(a) to yield a compressed dry air feed; cooling the compressed dry air feed in a heat exchanger; expanding a first portion of the compressed dry air feed in a cold turbine to form an expanded fluid; sending at least a portion of the expanded fluid to the higher-pressure column for separation therein; liquefying a second portion of the compressed dry air feed within the heat exchanger before sending at least a portion of the second portion of the compressed dry air feed to the higher-pressure column; sending an oxygen-rich liquid from a bottom portion of the higher-pressure column to an intermediate portion of the lower-pressure column; and sending a second oxygen-rich liquid from a bottom portion of the lower-pressure column to the second condenser, wherein at least a portion of the second oxygen-rich liquid is vaporized at less than 2 bar(a) to form a top gas, and wherein at least a portion of the top gas is warmed in the heat exchanger against the compressed dry air feed, mixing a first liquid nitrogen stream that was condensed by the first condenser with a second liquid nitrogen that was condensed by the second condenser to yield a liquid nitrogen product, wherein a lost air stream is warmed and expanded to less than 2 bar(a) in a warm turbine, wherein the lost air stream is selected from the group consisting of a portion of the expanded fluid from the cold turbine, a stream withdrawn from the higher-pressure column, and combinations thereof.

2. The process as claimed in claim 1, wherein the warm turbine has an inlet pressure substantially similar to an outlet pressure of the cold turbine.

3. The process as claimed in claim 1, wherein the higher-pressure column operates at a first pressure that is greater than 6.5 bar(a), wherein the second condenser operates at a third pressure that is less than 2 bar(a), wherein the lower-pressure column operates at a second pressure that is between the first pressure and the third pressure.

4. The process as claimed in claim 1, wherein the warm turbine has an inlet temperature and an outlet temperature and the cold turbine has an inlet temperature and an outlet temperature, wherein a temperature difference of the inlet and outlet temperatures of the warm turbine is greater than a temperature difference of the inlet and outlet temperatures of the cold turbine.

5. The process as claimed in claim 1, wherein the cold turbine drives a first compressor that is configured to further pressurize the compressed dry air feed prior to cooling in the heat exchanger.

6. The process as claimed in claim 2, wherein the warm turbine drives a second compressor that is configured to further pressurize the compressed dry air feed prior to cooling in the heat exchanger.

7. The process as claimed in claim 3, wherein the first and second compressors are arranged in parallel.

8. The process as claimed in claim 3, wherein the first and second compressors are arranged in series.

9. The process as claimed in claim 3, wherein the compressed dry air feed exiting at least one of the first and second compressors is at a pressure above 50 bar(a) prior to cooling in the heat exchanger.

10. The process as claimed in claim 1, wherein a main air compressor is disposed upstream of the purification unit and is configured to produce the feed air purified in the purification unit, wherein the main air compressor is the only compression means used in the process that relies on an external energy source for compression.

11. The process as claimed in claim 7, wherein the external energy source includes an electrical motor, steam turbine, and/or gas turbine.

12. The process as claimed in claim 1, wherein a ratio of fluid expanded in the warm turbine to compressed dry air feed is between 0.4 and 0.6, preferably between 0.45 and 0.5, and recovery of nitrogen as liquid nitrogen product as compared to total nitrogen sent to the higher-pressure column is between 0.55 and 0.65.

13. The process as claimed in claim 1, wherein a pressure ratio of the warm turbine is greater than 5.2 and less than 8, and wherein a ratio of a flow rate of the warm turbine to a flow rate of the cold turbine is greater than 0.6.

Description

BRIEF DESCRIPTION OF THE DRAWINGS

[0035] These and other features, aspects, and advantages of the present invention will become better understood with regard to the following description, claims, and accompanying drawings. It is to be noted, however, that the drawings illustrate only several embodiments of the invention and are therefore not to be considered limiting of the invention's scope as it can admit to other equally effective embodiments.

[0036] FIG. 1 provides an embodiment of the present invention.

[0037] FIG. 2 provides a heat diagram of an embodiment of the present invention.

[0038] FIG. 3 provides a heat diagram of an embodiment of the prior art.

DETAILED DESCRIPTION

[0039] While the invention will be described in connection with several embodiments, it will be understood that it is not intended to limit the invention to those embodiments. On the contrary, it is intended to cover all the alternatives, modifications and equivalence as may be included within the spirit and scope of the invention defined by the appended claims.

[0040] The terms nitrogen-rich and oxygen-rich will be understood by those skilled in the art to be in reference to the composition of air. As such, nitrogen-rich encompasses a fluid having a nitrogen content greater than that of air. Similarly, oxygen-rich encompasses a fluid having an oxygen content greater than that of air. Further, substantially similar to air is meant to encompass a stream having a similar composition as air (e.g., the ratio of nitrogen to oxygen is between 3:1 to 17:3, more preferably between 7:2 to 9:2) As used herein, substantially similar in pressure is a pressure that is similar to another pressure taking into account pressure losses in the system. In certain embodiments, this can be within 0.5 bar(a), more preferably within 0.3 bar(a), more preferably within 0.25 bar(a).

[0041] FIG. 1 illustrates a first embodiment of the cryogenic air separation process according to the present invention.

[0042] The process begins with atmospheric air 2 being drawn into the Main Air Compressor (MAC) 10 where it is compressed. The compressed air is then cooled in compressor after-cooler 20 before entering a front-end purification unit 30. This unit removes impurities such as water vapor and carbon dioxide that would freeze in the cryogenic temperatures of the main heat exchanger 80.

[0043] Following purification, the air stream is further compressed in boosters 40, 50 and cooled in associated after-coolers, resulting in a high-pressure air stream 52. This stream 52 enters the main heat exchanger 80 to be cryogenically cooled against returning process streams.

[0044] Inside the main heat exchanger 80, the cooling air stream 52 is divided. A first portion 54 continues through the main heat exchanger 80 until it is fully cooled near its cold end. This cold, high-pressure stream 54 is then expanded across an expansion valve 55 to generate Joule-Thomson cooling and potentially liquefaction, before being fed into the distillation column system. In certain embodiments, expansion valve 55 may be replaced by a liquid turbine. This system comprises a higher-pressure column 90, a lower-pressure column 100, and a top condenser 115.

[0045] A second portion 56 of the main air stream is withdrawn from an intermediate point within the main heat exchanger 80 at a warmer temperature than the first portion 54. This intermediate stream 56 is directed to the cold turbine 70, where it expands to generate refrigeration. The expanded, colder air exiting the cold turbine 70 is then fed via line 72 into the higher-pressure column 90 for separation therein. The outlet pressure of this cold turbine 70 is typically set to be approximately equal to the operating pressure of the higher-pressure column 90 (accounting for pressure losses within the system).

[0046] To provide additional refrigeration for the process, a warm turbine 60, functioning as a lost air or waste expansion turbine, is utilized. In the primary configuration shown, a stream 92, typically having a composition similar to air, is withdrawn from the higher-pressure column 90. This stream 92 is partially warmed by passing through the main heat exchanger 80 before being extracted from an intermediate point (or from the warm end of the main heat exchanger 80). It is then expanded across the warm turbine 60. The resulting cold, expanded fluid 62 is reintroduced into the main heat exchanger 80 to recover its remaining refrigeration by warming against incoming air, before being withdrawn from the warm end of the heat exchanger and potentially vented to the atmosphere.

[0047] Alternatively, the feed to the first turbine 60 can be sourced differently. Instead of using stream 92 from the column, a side stream 92a derived from the flow path after expansion in the cold turbine 70 can be directed to the warm turbine 60 to perform a similar refrigeration duty.

[0048] With respect to the system of columns, an oxygen-rich liquid 94 is withdrawn from a bottom portion of the higher-pressure column, subcooled, and expanded to the pressure of the lower-pressure column before being introduced into said lower-pressure column 100. The lower-pressure column 100 is thermally linked to the higher-pressure column 90 via a first condenser/reboiler 105, which is configured to condense gaseous nitrogen 91 against liquid oxygen collected in the bottom of the lower-pressure column 100 into liquid nitrogen 93. The liquid nitrogen 93 then flows back into the higher-pressure column 90 as a reflux stream.

[0049] A second oxygen-rich liquid 104 is withdrawn from the bottom section of the lower-pressure column 100 and then expanded to a pressure that is above atmospheric before being transferred to the top condenser/reboiler 115. This liquid oxygen-rich fluid vaporizes while condensing low-pressure gaseous nitrogen 101 into lower-pressure liquid nitrogen 103. A waste oxygen stream 112 is removed and then heated in the subcooler and then main heat exchanger 80. The stream 112 can be vented, or used as a regeneration gas for the front-end purification unit 30 (not shown).

[0050] Finally, the desired liquid nitrogen product 106 is collected from the process, potentially being drawn from one or both the lower-pressure column 100 and the higher-pressure column 90, via lines 102 and 96, respectively.

[0051] While the present invention shares some visual similarities with prior art systems, such as the one depicted in FIG. 2 of U.S. Pat. No. 9,726,427 ('427), several key operational differences lead to distinct advantages, particularly in refrigeration capacity. Notably, unlike the '427 patent, certain embodiments of the present invention do not require a booster air compressor (105).

[0052] A more significant distinction lies in the operating conditions of the turbine system. Although the turbo-booster arrangement in '427 (turbines 107/112 and compressors 109/111) appears similar, the present invention operates its cold turbine and warm turbine under conditions optimized for enhanced refrigeration.

[0053] Designing cryogenic liquefaction units involves navigating practical equipment limitations. For instance, commonly used brazed-aluminum heat exchangers generally have a maximum operating pressure of about 70 bar(a). Turbines also face constraints, typically limited to a pressure expansion ratio of around 12. In prior art systems like '427, these limits dictate that the maximum inlet pressure to the cold turbine is 70 bar(a), resulting in a minimum outlet pressure of approximately 5.83 bar(a) when operating at maximum capacity (70 bar(a), pressure ratio of 12). This pressure constraint inherently limits the refrigeration potential achievable through turbine expansion.

[0054] Furthermore, conventional cryogenic plant design often sets column pressures relative to atmospheric pressure. Typically, the lowest pressure section operates slightly above atmospheric, the medium-pressure column operates 2-4 bar(a) higher, and the high-pressure column operates another 2-4 bar(a) above that. The '427 patent exemplifies this, with a top condenser at 1.28 bar(a), a low-pressure column at 3.2 bar(a), and a high-pressure column around 5.2 bar(a).

[0055] In the '427 design, both turbines discharge at essentially the same pressure (approximately 6.05 bar(a)). This is because their outlet streams (22) are combined and fed to the booster air compressor (105). This configuration restricts the operational flexibility of the warm turbine (111), largely fixing its inlet and outlet pressures based on the overall plant requirements. Consequently, the pressure ratio across this warm turbine in '427 is limited to 5.0, yielding a temperature drop of approximately 84 C.

[0056] Conversely, embodiments of the present invention optimize the system differently. The warm turbine 60 is configured to discharge at a significantly lower pressure, typically just above atmospheric (e.g., 1.25 bar(a) as shown in Table II). This allows for a considerably higher pressure ratio across this turbine compared to the prior art. For example, an illustrative embodiment achieves a pressure ratio of 5.8. While the numerical difference between 5.8 and 5.0 may seem modest, it results in a substantially larger temperature drop across the turbine 97 C. in this example, compared to 84 C. in '427. This increased temperature drop translates directly to greater refrigeration capacity generated by this turbine stage.

[0057] Table II below presents comparative data for three prior art cryogenic facilities alongside an illustrative embodiment of the present invention (FIG. 1):

TABLE-US-00002 TABLE II Comparison data Single column, single U.S. Pat. No. GOK condenser 9,726,427 (Lost Air) FIG. 1 Plant type N2 plant N2 plant O2 plant N2 plant Warm inlet pressure (bar(a)) 4 31 6.1 7.25 turbine outlet pressure 1.2 6.15 1.25 1.25 (LP (bar(a)) Turbine) Pressure ratio 3.3 5.0 4.9 5.8 temperature difference 70 84 82 97 ( C.) Cold inlet pressure (bar(a)) 48 64.1 64.5 64.5 turbine outlet pressure 4 6.15 6.1 7.4 (HP (bar(a)) Turbine) Pressure ratio 12 10.4 10.6 8.7 temperature difference 89 93 100 82 ( C.) HP pressure (bar(a)) 5.2 6.1 7.4 Column LP Column pressure (bar(a)) 3.2 1.3 4

[0058] As highlighted in Table II, prior art examples typically maximize the pressure drop (and thus temperature difference) across the cold turbine. In contrast, the present invention shifts a larger portion of the refrigeration duty to the warm (or lower-pressure) turbine by maximizing its pressure ratio and temperature drop.

[0059] A key consequence of this approach is that the cold turbine (e.g., higher pressure turbine) in the present invention operates with a lower pressure ratio (e.g., 8.7 compared to 10.4-12 in the prior art). This reduced expansion allows the cold turbine's outlet pressure to be significantly higher (e.g., 7.4 bar(a) vs. 6.1 bar(a)). This higher pressure stream feeds the distillation columns, enabling operation of both the higher-pressure and lower-pressure columns at elevated pressures compared to traditional designs.

[0060] The operating pressures of the columns of a double column, double condenser process as described herein and in FIG. 2 of prior art '427 are the result of several parameters. For example, the pressure of the waste stream vaporized in top condenser/vaporizer is determined by the pressure drop to atmosphere, and the pressures of the low pressure and high pressure columns are the result of the compositions of streams being condensed and vaporized in both of the condenser/vaporizers Finally, by increasing the temperature difference between inlet and outlet of the warm turbine and reducing the temperature difference between inlet and outlet of the cold turbine embodiments of the present invention can also experience reduced heat transfer losses in the main heat exchanger, further contributing to overall efficiency. This is because the narrower temperature range of the cold turbine allows its refrigeration to be placed in the section of the air condensing phase change where refrigeration is needed. Whereas, the wider temperature range of the warm turbine can be spread over the warm section where the heat transfer curves are more linear because there is no phase change.

[0061] Furthermore, by strategically adjusting the distribution of refrigeration load, as well as warm and cold turbine temperatures and pressures, embodiments of the present invention achieve reduced overall heat transfer losses within the main heat exchanger. This benefit is particularly impactful in the cold section of the exchanger. Visual representations, such as the temperature approach curves shown in FIG. 2 and FIG. 3, illustrate this effect; the area between the heating and cooling curves in the cold section is smaller for the present invention, signifying reduced thermodynamic losses.

[0062] While the prior art system ('427) may exhibit a slightly smaller temperature difference (and thus higher efficiency) in the warm section of the heat exchanger, optimizing performance at the cold end is more critical for maximizing the overall efficiency of cryogenic processes, since colder refrigeration is more expensive to produce.

[0063] It is known that the areas between the heating and cooling curves represent irreversible losses (inefficiency) of the heat exchange process. At a high level, comparing the max dT in each section can give an indication of this efficiency loss. Therefore, effective heat transfer aims to minimize the temperature difference (dT) between the exchanging streams throughout the exchanger.

[0064] Table III provides a comparison of the maximum temperature differences (Max dT) within key sections of the main heat exchanger for an embodiment of the present invention versus the '427 design:

TABLE-US-00003 TABLE III Comparison Data of dT in Main Heat Exchanger FIG. 1 of Present FIG. 2 Application of 427 Cold Section 9.5 10.1 Max dT ( C.) Mid section 10.5 15 Max dT ( C.) Warm 6.8 4 Section Max dT ( C.)

[0065] As indicated in Table III, the present invention achieves smaller maximum temperature differences in the cold section (9.5 C. vs 10.1 C.) and the middle section (10.5 C. vs 15 C.) compared to the '427 configuration. Although the '427 design shows a tighter temperature approach in the warm section (4 C. vs 6.8 C.), the enhanced performance of the present invention in the colder, thermodynamically more sensitive sections contributes significantly to its improved overall efficiency compared to the prior art.

[0066] Conventional Main Air Compressor (MAC) comprise intercoolers and an after cooler where cooling water supply (e.g. from evaporative tower and/or closed loop cooling system) cools the air to near atmospheric temperature. Some water is condensed in the intercoolers and after cooler and removed from the system. The quantity of remaining entrained moisture content in the saturated compressed air exiting the after cooler increases with increasing temperature and reduces with increasing pressure. For example, saturated air at 30 C. and 6.4 bar(a) contains 5.47 kg water/KNm.sup.3 air.

[0067] Sizing a purification system for such water content would yield very large and possibly unfeasible adsorbers for large flows. The conventional solution is adding a precooling system to cool the compressed air. For example 5.8 C. and 6.4 bar(a) yields 1.18 kg water/KNm.sup.3 air. However, a high pressure air system at 30 C., 32 bar(a) also yields 1.18 kg water/KNm.sup.3 air (same water content in compressed air but no precooling). In addition, the volumetric flowrate is inversely proportional to pressure. Thus, equipment size and piping at 32 bar is five times smaller than a purification system at 6.4 bar and passing the same mass flowrate.

[0068] Certain embodiments of the present invention have 3 to 4% lower power consumption for same net production (i.e., 3 to 4% improved efficiency) compared to prior art '427. In addition, certain embodiments of the present invention have significantly lower equipment cost due to (1) one compressor (1HPMAC) rather than two compressors (1MAC+1BAC), (2) smaller adsorbers, and (3) optionally no precooling.

[0069] While the invention has been described in conjunction with specific embodiments thereof, it is evident that many alternatives, modifications, and variations will be apparent to those skilled in the art in light of the foregoing description. Accordingly, it is intended to embrace all such alternatives, modifications, and variations as fall within the spirit and broad scope of the appended claims. The present invention may suitably comprise, consist or consist essentially of the elements disclosed and may be practiced in the absence of an element not disclosed. Furthermore, if there is language referring to order, such as first and second, it should be understood in an exemplary sense and not in a limiting sense. For example, it can be recognized by those skilled in the art that certain steps can be combined into a single step.

[0070] The singular forms a, an and the include plural referents, unless the context clearly dictates otherwise.

[0071] Comprising in a claim is an open transitional term which means the subsequently identified claim elements are a nonexclusive listing (i.e., anything else may be additionally included and remain within the scope of comprising). Comprising as used herein may be replaced by the more limited transitional terms consisting essentially of and consisting of unless otherwise indicated herein.

[0072] Providing in a claim is defined to mean furnishing, supplying, making available, or preparing something. The step may be performed by any actor in the absence of express language in the claim to the contrary.

[0073] Optional or optionally means that the subsequently described event or circumstances may or may not occur. The description includes instances where the event or circumstance occurs and instances where it does not occur.

[0074] Ranges may be expressed herein as from about one particular value, and/or to about another particular value. When such a range is expressed, it is to be understood that another embodiment is from the one particular value and/or to the other particular value, along with all combinations within said range.

[0075] All references identified herein are each hereby incorporated by reference into this application in their entireties, as well as for the specific information for which each is cited.